Steam-jet mixer outlet pressure stabilizing and adjusting method and system

Abstract

The present application relates to the technical field of steam jet mixers, and specifically discloses a steam jet mixer outlet pressure stabilizing and adjusting method and system. The present application obtains high-pressure steam inlet pressure, low-pressure steam inlet pressure and outlet pressure actual values, obtains reference driving pressure and high-pressure steam fluctuation data according to high-pressure steam inlet pressure data, obtains driving pressure dynamic response coefficients in combination with pressure transient deviation, fluctuation root mean square values and high-frequency fluctuation energy proportion, obtains injection end pressure values and injection flow data according to low-pressure steam inlet pressure data, then obtains injection structure sensitivity coefficients, fuses the driving pressure dynamic response coefficients and the injection structure sensitivity coefficients to obtain high-pressure side driving capability coefficients, obtains downstream load disturbance coefficients, and obtains outlet pressure dynamic balance coefficients according to the high-pressure side driving capability coefficients and the downstream load disturbance coefficients, thereby adjusting the high-pressure steam inlet valve opening degree for dynamic balance adjustment, and solving the problem of response lag in the prior art.

Description

Technical Field

[0001] This invention relates to the field of steam jet mixer technology, and in particular to a method and system for regulating the outlet pressure of a steam jet mixer. Background Technology

[0002] A steam jet mixer is a device that uses high-pressure steam (working steam) as a power source to generate a high-speed jet through nozzles, thereby drawing in and mixing low-pressure steam (ejector steam). It is widely used in industrial heating, thermal system optimization, and waste heat recovery. Its main function is to mix steam of different pressure levels and output mixed steam that meets specific pressure and temperature requirements.

[0003] Existing technologies for regulating the outlet pressure of steam jet mixers generally employ PID control methods based on single outlet pressure feedback, maintaining stable outlet pressure by adjusting the opening of the high-pressure steam inlet valve. However, existing PID control relies on a negative feedback mechanism of "adjusting only after an error occurs." When the downstream steam load changes abruptly, the outlet pressure fluctuates before the control system responds, resulting in a lag in the adjustment action. Therefore, a new method for stabilizing and regulating the outlet pressure of steam jet mixers is needed to address this problem. Summary of the Invention

[0004] The purpose of this invention is to provide a method for regulating the outlet pressure of a steam jet mixer, comprising: Obtain the operating parameters of the steam jet mixer, wherein the operating parameters include high-pressure steam inlet pressure data, low-pressure steam inlet pressure data, and actual outlet pressure values; The reference driving pressure and high-pressure steam fluctuation data are obtained based on the high-pressure steam inlet pressure data, and the dynamic response coefficient of the driving pressure is obtained based on the reference driving pressure and high-pressure steam fluctuation data. The ejector end pressure value and ejector flow rate data are obtained based on the low-pressure steam inlet pressure data, and the ejector structure sensitivity coefficient is obtained based on the ejector end pressure value and ejector flow rate data. The high-pressure side driving capability coefficient is obtained based on the driving pressure dynamic response coefficient and the ejector structure sensitivity coefficient. The real-time outlet pressure sequence and pressure fluctuation spectrum are obtained based on the actual outlet pressure value, and the downstream load disturbance coefficient is obtained based on the real-time outlet pressure sequence and the pressure fluctuation spectrum. The outlet pressure dynamic balance coefficient is obtained based on the high-pressure side driving capability coefficient and the downstream load disturbance coefficient, and the outlet pressure of the steam jet mixer is adjusted based on the outlet pressure dynamic balance coefficient.

[0005] Preferably, the step of obtaining the dynamic response coefficient of the driving pressure based on the reference driving pressure and the high-pressure steam fluctuation data includes: Acquire historical pressure time series data of the high-pressure steam inlet within a preset historical time period, and obtain the pressure reference stable value of the high-pressure steam based on the historical pressure time series data, and use the pressure reference stable value as the reference driving pressure. The real-time pressure value at the current moment is obtained based on the high-pressure steam inlet pressure data, and the pressure transient deviation value is obtained based on the real-time pressure value and the reference driving pressure. The pressure data at the high-pressure steam inlet is sampled within a unit time window to obtain a pressure instantaneous fluctuation sequence. The root mean square value of the fluctuation is calculated based on the pressure instantaneous fluctuation sequence, and the root mean square value of the fluctuation is used as the high-pressure steam fluctuation data. The pressure response amplitude factor is obtained based on the pressure transient deviation value and the root mean square value of the fluctuation, and a fast Fourier transform is performed on the pressure instantaneous fluctuation sequence to obtain the fluctuation spectrum energy distribution. The proportion of high-frequency fluctuation energy is obtained based on the fluctuation spectrum energy distribution. The driving pressure dynamic response coefficient is obtained based on the pressure response amplitude factor and the proportion of high-frequency fluctuation energy.

[0006] Preferably, the step of obtaining the sensitivity coefficient of the ejector structure based on the ejector end pressure value and the ejector flow rate data includes: Obtain the pressure sequence of the low-pressure steam inlet within a continuous time window, calculate the pressure change rate sequence based on the pressure sequence, and use the current value of the pressure sequence as the ejector end pressure value. Obtain the geometric parameters of the mixer ejector cavity, and calculate the theoretical maximum ejector flow rate based on the geometric parameters and the ejector end pressure value, and use the theoretical maximum ejector flow rate as the reference ejector flow rate; Obtain the real-time flow rate detection value of the low-pressure steam inlet, and obtain the flow rate deviation ratio based on the real-time flow rate detection value and the reference ejector flow rate; Kalman filtering is applied to the pressure change rate sequence to obtain a smoothed pressure change rate, and the flow resistance change gradient of the ejector cavity is obtained based on the smoothed pressure change rate and the flow deviation ratio. The sensitivity coefficient of the ejector structure is obtained based on the flow resistance variation gradient and the geometric parameters of the ejector cavity.

[0007] Preferably, the step of obtaining the high-pressure side driving capability coefficient based on the driving pressure dynamic response coefficient and the ejector structure sensitivity coefficient includes: Obtain the nozzle throat area parameters and nozzle outlet area parameters of the high-pressure steam inlet, and calculate the nozzle expansion ratio based on the nozzle throat area parameters and the nozzle outlet area parameters; The jet flow correction factor for high-pressure steam is obtained based on the driving pressure dynamic response coefficient and the expansion ratio. The momentum exchange efficiency coefficient of the mixing chamber is obtained based on the sensitivity coefficient of the ejector structure and the ejector momentum correction factor. The high-pressure side driving capability coefficient is obtained based on the momentum exchange efficiency coefficient and the real-time pressure value of the high-pressure steam inlet.

[0008] Preferably, the step of obtaining the real-time outlet pressure sequence and pressure fluctuation spectrum based on the actual outlet pressure value, and obtaining the downstream load disturbance coefficient based on the real-time outlet pressure sequence and the pressure fluctuation spectrum, includes: The actual value of the outlet pressure is continuously collected at a preset sampling frequency to obtain the real-time outlet pressure sequence. Empirical mode decomposition is performed on the real-time outlet pressure sequence to obtain multiple intrinsic mode function components, and the intrinsic mode function components with frequencies higher than the preset cutoff frequency are taken as high-frequency pressure fluctuation components. The high-frequency pressure fluctuation components are subjected to Hilbert transform to obtain the instantaneous pressure fluctuation amplitude sequence and the instantaneous pressure fluctuation frequency sequence; The cumulative pressure fluctuation energy per unit time is calculated based on the instantaneous pressure fluctuation amplitude sequence, and the dominant frequency offset of the pressure fluctuation is calculated based on the instantaneous pressure fluctuation frequency sequence. The downstream load disturbance coefficient is obtained based on the cumulative value of the pressure fluctuation energy and the main frequency offset of the pressure fluctuation.

[0009] Preferably, the step of obtaining the outlet pressure dynamic balance coefficient based on the high-pressure side drive capability coefficient and the downstream load disturbance coefficient, and adjusting the outlet pressure of the steam jet mixer based on the outlet pressure dynamic balance coefficient, includes: The theoretical maximum output pressure of the high-pressure side under the current operating conditions is obtained based on the high-pressure side drive capability coefficient, and the theoretical maximum output pressure is used as the upper limit of the drive pressure. The downstream pressure bearing margin under the current operating conditions is obtained based on the downstream load disturbance coefficient, and the pressure bearing margin is used as the disturbance pressure tolerance value. The pressure regulation safety boundary is obtained based on the upper limit of the driving pressure and the disturbance pressure tolerance value; Obtain a preset target pressure setting value, and obtain an outlet pressure dynamic balance coefficient based on the pressure adjustment safety boundary and the target pressure setting value, wherein the outlet pressure dynamic balance coefficient is a normalized value of the ratio of the upper limit of the driving pressure to the disturbance pressure tolerance value under the constraint of the target pressure setting value. A valve opening adjustment command is generated based on the outlet pressure dynamic balance coefficient, and the opening of the high-pressure steam inlet valve is controlled according to the valve opening adjustment command so that the actual pressure value at the mixer outlet approaches the target pressure setting value.

[0010] This application also provides a steam jet mixer outlet pressure stabilization and regulation system, including: The first acquisition module is used to acquire the operating parameters of the steam jet mixer, wherein the operating parameters include high-pressure steam inlet pressure data, low-pressure steam inlet pressure data and actual outlet pressure values; The second acquisition module is used to acquire the reference driving pressure and high-pressure steam fluctuation data based on the high-pressure steam inlet pressure data, and to acquire the driving pressure dynamic response coefficient based on the reference driving pressure and high-pressure steam fluctuation data. The third acquisition module is used to acquire the ejector end pressure value and ejector flow rate data based on the low-pressure steam inlet pressure data, and to acquire the ejector structure sensitivity coefficient based on the ejector end pressure value and ejector flow rate data. The fourth acquisition module is used to acquire the high-pressure side driving capability coefficient based on the driving pressure dynamic response coefficient and the ejector structure sensitivity coefficient. The fifth acquisition module is used to acquire a real-time outlet pressure sequence and pressure fluctuation spectrum based on the actual outlet pressure value, and to acquire a downstream load disturbance coefficient based on the real-time outlet pressure sequence and the pressure fluctuation spectrum. The adjustment module is used to obtain the outlet pressure dynamic balance coefficient based on the high-pressure side drive capability coefficient and the downstream load disturbance coefficient, and to adjust the outlet pressure of the steam jet mixer based on the outlet pressure dynamic balance coefficient.

[0011] Preferably, the second acquisition module includes: The first acquisition unit is used to acquire historical pressure time series data of the high-pressure steam inlet within a preset historical time period, and to acquire the pressure reference stable value of the high-pressure steam based on the historical pressure time series data, and to use the pressure reference stable value as the reference driving pressure. The second acquisition unit is used to acquire the real-time pressure value at the current moment based on the high-pressure steam inlet pressure data, and to acquire the pressure transient deviation value based on the real-time pressure value and the reference driving pressure. The sampling unit is used to perform sliding sampling on the high-pressure steam inlet pressure data within a unit time window to obtain a pressure instantaneous fluctuation sequence, and to calculate the root mean square value of the fluctuation based on the pressure instantaneous fluctuation sequence, and to use the root mean square value of the fluctuation as the high-pressure steam fluctuation data. The third acquisition unit is used to acquire the pressure response amplitude factor based on the pressure transient deviation value and the root mean square value of the fluctuation, and to perform a fast Fourier transform on the pressure instantaneous fluctuation sequence to obtain the fluctuation spectrum energy distribution, and to acquire the proportion of high-frequency fluctuation energy based on the fluctuation spectrum energy distribution. The fourth acquisition unit is used to acquire the dynamic response coefficient of the driving pressure based on the pressure response amplitude factor and the proportion of high-frequency fluctuation energy.

[0012] This application also provides a computer device, including a memory and a processor, wherein the memory stores a computer program, and the processor executes the computer program to implement the steps of the above-described method.

[0013] This application also provides a computer-readable storage medium having a computer program stored thereon, which, when executed by a processor, implements the steps of the above-described method.

[0014] The beneficial effects of this application are as follows: This invention acquires high-pressure steam inlet pressure data, low-pressure steam inlet pressure data, and actual outlet pressure values ​​in real time, constructs a quantitative evaluation system based on multi-source data fusion, and dynamically optimizes outlet pressure regulation. First, raw data is collected from steam source pressure sensors, ejector chamber pressure sensors, and outlet pressure sensors, covering core information such as high-pressure side pressure status, ejector side flow characteristics, and outlet side fluctuation characteristics. Then, through collaborative analysis of pressure transient deviation and root mean square value of fluctuation, and extraction of fast Fourier transform spectral features, the dynamic response coefficient of the driving pressure is calculated, characterizing the pressure recovery capability of the high-pressure steam source under unit disturbance; through Kalman filtering and flow resistance change gradient analysis, the sensitivity coefficient of the ejector structure is calculated, quantifying the nonlinear response of the ejector chamber to flow rate under different pressure differences; by fusing the above two coefficients, the driving capability coefficient of the high-pressure side is calculated, characterizing the actual entrainment capability of the high-pressure steam jet on low-pressure steam in the mixing chamber; through empirical mode decomposition and Hilbert transform, the outlet pressure fluctuation characteristics are extracted, and the downstream load disturbance coefficient is calculated, quantifying the reaction strength of downstream steam-using equipment on the mixer outlet pressure. Finally, the high-pressure side driving capability coefficient and the downstream load disturbance coefficient are integrated into the outlet pressure dynamic balance coefficient to achieve dynamic balance between the high-pressure side driving capability and the downstream load disturbance, generate valve opening adjustment commands, and achieve precise pressure stabilization and regulation of the outlet pressure. Attached Figure Description

[0015] Figure 1 This is a schematic diagram of a method flow according to an embodiment of this application.

[0016] Figure 2 This is a schematic diagram of the system structure according to an embodiment of this application.

[0017] The purpose, features, and advantages of this application will be further explained in conjunction with the embodiments and with reference to the accompanying drawings. Detailed Implementation

[0018] It should be understood that the specific embodiments described herein are merely illustrative of the invention and are not intended to limit the invention.

[0019] like Figure 1 As shown, this application provides a method for regulating the outlet pressure of a steam jet mixer, comprising: S1. Obtain the operating parameters of the steam jet mixer, wherein the operating parameters include high-pressure steam inlet pressure data, low-pressure steam inlet pressure data, and actual outlet pressure value; S2. Obtain the reference driving pressure and high-pressure steam fluctuation data based on the high-pressure steam inlet pressure data, and obtain the driving pressure dynamic response coefficient based on the reference driving pressure and high-pressure steam fluctuation data; S3. Obtain the ejector end pressure value and ejector flow rate data based on the low-pressure steam inlet pressure data, and obtain the ejector structure sensitivity coefficient based on the ejector end pressure value and ejector flow rate data; S4. Obtain the high-pressure side driving capability coefficient based on the driving pressure dynamic response coefficient and the ejector structure sensitivity coefficient; S5. Obtain the real-time outlet pressure sequence and pressure fluctuation spectrum based on the actual outlet pressure value, and obtain the downstream load disturbance coefficient based on the real-time outlet pressure sequence and the pressure fluctuation spectrum. S6. Obtain the outlet pressure dynamic balance coefficient based on the high-pressure side driving capability coefficient and the downstream load disturbance coefficient, and adjust the outlet pressure of the steam jet mixer based on the outlet pressure dynamic balance coefficient.

[0020] As described in steps S1-S6 above, existing technologies for regulating the outlet pressure of steam jet mixers often employ a single outlet pressure feedback-based adjustment method. The core problem with this method is that it relies solely on the actual deviation of the outlet pressure for reactive adjustment, failing to capture the dynamic trends of the high-pressure side, low-pressure side, and downstream load in advance. When the downstream steam load undergoes a sudden change or the high-pressure and low-pressure steam parameters fluctuate, the outlet pressure will fluctuate significantly before the control system can respond, resulting in a significant lag in the adjustment action. This makes it difficult to meet the high-precision requirements for stable steam pressure in industrial scenarios. Therefore, this invention obtains the operating parameters of the steam jet mixer, including high-pressure steam inlet pressure data, low-pressure steam inlet pressure data, and the actual outlet pressure value. This step is the foundation of the entire pressure stabilization and regulation method; all subsequent coefficient calculations and adjustment actions are based on the raw data obtained in this step. The high-pressure steam inlet pressure data is collected in real time by a pressure sensor installed at the high-pressure steam inlet. The low-pressure steam inlet pressure data is continuously detected and acquired by the pressure sensor at the ejector chamber, while the actual outlet pressure value is collected by the pressure sensor at the mixer outlet at a preset sampling frequency. The acquisition of all three types of data is uninterrupted real-time, ensuring accurate capture of the dynamic pressure changes at key locations of the mixer. This provides real and continuous raw data support for subsequent quantitative analysis. The physical significance of this step is to open up the data acquisition channels for each key operating link of the mixer, transforming the physical operating status of the equipment into quantifiable numerical parameters. This enables a comprehensive perception of the mixer's operating status from a data perspective. For example, in an industrial heating scenario, the high-pressure steam inlet pressure drops from 0.8MPa to 0.75MPa due to boiler steam supply fluctuations, the low-pressure steam inlet pressure rises from 0.2MPa to 0.22MPa due to pipeline changes, and the actual outlet pressure drops from 0.3MPa to 0.28MPa. These pressure changes can all be captured in real time by the corresponding sensors and converted into data parameters, providing a basis for subsequent analysis.

[0021] Based on the high-pressure steam inlet pressure data, a reference driving pressure and high-pressure steam fluctuation data are obtained. Then, the dynamic response coefficient of the driving pressure is obtained based on these data. This step is a quantitative analysis of the dynamic characteristics of the high-pressure steam side driving capability. First, the stable pressure value within a preset historical time period is extracted from the historical time-series data collected by the high-pressure steam inlet pressure sensor as the reference driving pressure. This reference driving pressure serves as a standard to measure whether the high-pressure steam inlet pressure deviates from its normal state. Next, the pressure transient deviation value is calculated by the difference between the current real-time pressure value and the reference driving pressure, reflecting the instantaneous deviation of the high-pressure steam inlet pressure. Simultaneously, sliding sampling is performed on the high-pressure steam inlet pressure data within a unit time window to obtain the instantaneous pressure fluctuation sequence, and its root mean square value is calculated as the high-pressure steam fluctuation data, characterizing the intensity of the high-pressure steam inlet pressure fluctuation. Subsequently, the pressure response amplitude factor is obtained by combining the pressure transient deviation value and the root mean square value of the fluctuation. Then, a fast Fourier transform is performed on the instantaneous pressure fluctuation sequence to obtain the fluctuation spectrum energy distribution and extract the proportion of high-frequency fluctuation energy. Finally, the dynamic response coefficient of the driving pressure is calculated by fusing the pressure response amplitude factor and the proportion of high-frequency fluctuation energy. The physical meaning of this coefficient lies in characterizing the pressure recovery capability of the high-pressure steam source under a unit disturbance. The higher the coefficient value, the stronger the recovery capability of the high-pressure steam source to cope with pressure disturbances, and vice versa. For example, when the high-pressure steam inlet pressure fluctuates frequently and slightly due to steam source disturbances, the root mean square value of the fluctuation is small, and the pressure transient deviation value is also within a small range, the calculated dynamic response coefficient of the driving pressure is high, indicating that the pressure state on the high-pressure steam side is relatively stable and the dynamic change of the driving capability is small. This step, through multi-dimensional quantitative analysis of the high-pressure steam inlet pressure, transforms the dynamic change characteristics of the pressure on the high-pressure side into a single coefficient index, realizing the accurate quantification of the dynamic change of the high-pressure steam driving capability, and providing a reference quantitative basis for subsequent analysis of the impact of the high-pressure side on the outlet pressure.

[0022] Based on the low-pressure steam inlet pressure data, the ejector end pressure and ejector flow rate data are obtained. Then, the ejector structure sensitivity coefficient is calculated based on these data. This step quantitatively analyzes the ejector characteristics on the low-pressure steam side, precisely capturing the dynamic characteristics of the mixer ejector process. First, the current value is extracted as the ejector end pressure value from the continuous pressure sequence collected by the low-pressure steam inlet pressure sensor, and the pressure change rate sequence is calculated to reflect the changing trend of the ejector end pressure. Then, combined with the geometric parameters of the mixer ejector cavity and the ejector end pressure value, fluid dynamics formulas are used to calculate... The theoretical maximum ejector flow rate is calculated as the baseline ejector flow rate, which serves as a reference for evaluating the reasonableness of the actual ejector flow rate. Simultaneously, the real-time flow rate of the low-pressure steam inlet is obtained through a flow sensor, and the flow deviation ratio between the actual ejector flow rate and the baseline ejector flow rate is calculated to reflect the degree of deviation between the actual ejector flow rate and the theoretical value. Subsequently, the pressure change rate sequence is processed by Kalman filtering to eliminate data noise and obtain a smooth pressure change rate. Combined with the flow deviation ratio, the flow resistance change gradient of the ejector cavity is calculated. Finally, the flow resistance change gradient and the geometric parameters of the ejector cavity are fused to obtain the ejector structure sensitivity coefficient. The physical significance of this coefficient lies in quantifying the nonlinear response of the ejector cavity to flow rate under different pressure differentials. The higher the coefficient value, the more sensitive the flow rate of the ejector cavity is to changes in pressure differential, and vice versa. For example, when the flow resistance of the ejector cavity increases due to scaling or other reasons, and the flow resistance gradient increases, the calculated sensitivity coefficient of the ejector structure will increase accordingly. This indicates that a small change in the pressure at the ejector end will cause a significant change in the ejector flow rate. This step eliminates data interference through algorithms such as Kalman filtering and, combined with the physical structural parameters of the ejector cavity, completes the quantification of ejector characteristics. It transforms the dynamic changes of the low-pressure side ejector link into quantifiable coefficient indicators, realizing accurate analysis of the ejector structure response characteristics and providing quantitative support for subsequent analysis of the impact of the low-pressure side on the outlet pressure.

[0023] The high-pressure side driving capability coefficient is obtained by using the dynamic response coefficient of the driving pressure and the sensitivity coefficient of the ejector structure. This step is a comprehensive quantification of the actual driving capability of the high-pressure side, realizing the fusion analysis of the dynamic characteristics of the driving pressure on the high-pressure side and the response characteristics of the ejector structure on the low-pressure side. First, the throat area parameter and nozzle outlet area parameter of the high-pressure steam inlet nozzle are extracted, and the nozzle expansion ratio is calculated through geometric ratio. This parameter reflects the expansion characteristics of the high-pressure steam after passing through the nozzle and is a key physical parameter affecting the high-pressure steam jet flow rate. Then, combined with the dynamic response coefficient of the driving pressure and the nozzle expansion ratio, the jet flow rate correction factor of the high-pressure steam is calculated to correct the theoretical jet flow rate of the high-pressure steam, making it more consistent with the actual operating state of the equipment. Subsequently, the momentum exchange efficiency coefficient of the mixing chamber is obtained by merging the sensitivity coefficient of the ejector structure and the jet flow rate correction factor. This coefficient characterizes the momentum exchange efficiency between the high-pressure steam jet and the low-pressure steam in the mixing chamber and is a key indicator for measuring the mixing effect of the mixer. Finally, the high-pressure side driving capability coefficient is calculated by combining the momentum exchange efficiency coefficient and the real-time pressure value of the high-pressure steam inlet. The physical meaning of this coefficient lies in characterizing the actual entrainment capacity of the high-pressure steam jet on the low-pressure steam in the mixing chamber. The higher the coefficient value, the stronger the entrainment capacity of the high-pressure steam on the low-pressure steam, and the better the ejector mixing effect of the mixer. For example, when the dynamic response coefficient of the driving pressure is high and the nozzle expansion ratio is suitable, the jet momentum correction factor is within a reasonable range. The momentum exchange efficiency coefficient calculated by combining the ejector structure sensitivity coefficient is high, and the final high-pressure side driving capability coefficient is also correspondingly high. This indicates that the high-pressure side can provide strong power support for ejector mixing. This step, by integrating the two types of core coefficients obtained in the previous steps and combining them with the physical structural parameters of the nozzle and mixing chamber, completes the comprehensive quantification of the actual driving capability of the high-pressure side. It integrates the key influencing factors of the high-pressure side and the low-pressure side into a single coefficient index, laying the foundation for subsequent analysis of the impact of the overall operating state of the mixer on the outlet pressure.

[0024] The real-time outlet pressure sequence and pressure fluctuation spectrum are obtained based on the actual outlet pressure value. The downstream load disturbance coefficient is then obtained from these parameters. This step involves a quantitative analysis of the downstream load disturbance characteristics, accurately capturing the impact of downstream steam load changes on the mixer outlet pressure. First, the actual outlet pressure value is continuously collected at a preset sampling frequency to form a real-time outlet pressure sequence, completely recording the dynamic change process of the outlet pressure. Then, empirical mode decomposition is performed on the real-time outlet pressure sequence, decomposing it into multiple intrinsic mode function components. Components with frequencies higher than the preset cutoff frequency are extracted as high-frequency pressure fluctuations. The system focuses on high-frequency fluctuations that reflect sudden changes in downstream load. A Hilbert transform is then applied to these high-frequency pressure fluctuation components to obtain instantaneous pressure fluctuation amplitude and frequency sequences, reflecting the amplitude and frequency variations of the high-frequency outlet pressure fluctuations, respectively. The cumulative pressure fluctuation energy per unit time is then calculated based on the instantaneous pressure fluctuation amplitude sequence to characterize the energy intensity of the downstream load disturbance. The dominant frequency offset of the pressure fluctuation is calculated based on the instantaneous pressure fluctuation frequency sequence to reflect the frequency characteristic changes of the downstream load disturbance. Finally, the cumulative pressure fluctuation energy and the dominant frequency offset are fused to calculate the downstream load disturbance coefficient. The physical meaning of this coefficient lies in quantifying the reaction strength of downstream steam-consuming equipment on the mixer outlet pressure. The higher the coefficient value, the greater the impact of downstream load disturbance on the outlet pressure, and vice versa. For example, when downstream steam-consuming equipment suddenly increases its steam consumption, the outlet pressure experiences high-frequency and large-amplitude fluctuations, the cumulative value of pressure fluctuation energy increases significantly, and the main frequency offset also exceeds the normal range. The calculated downstream load disturbance coefficient will increase accordingly, indicating that the downstream load has a strong disturbance effect on the outlet pressure at this time. This step uses algorithms such as empirical mode decomposition and Hilbert transform to refine and analyze the fluctuation characteristics of the outlet pressure, transforming the disturbance characteristics of the downstream load into quantifiable coefficient indicators, realizing accurate judgment of the degree of downstream load disturbance, and providing a quantitative basis for subsequent pressure regulation targeting downstream disturbances.

[0025] The dynamic balance coefficient of the outlet pressure is obtained based on the high-pressure side driving capability coefficient and the downstream load disturbance coefficient. The outlet pressure of the steam jet mixer is then adjusted according to this dynamic balance coefficient. This step is the core execution link of the entire pressure stabilization and regulation method, realizing the implementation from parameter analysis to pressure regulation. First, based on the high-pressure side driving capability coefficient, the theoretical maximum output pressure of the high-pressure side under the current operating conditions is calculated using relevant fluid mechanics formulas. This is used as the upper limit of the driving pressure, representing the maximum pressure support that the high-pressure side can provide to the mixer. Next, based on the downstream load disturbance coefficient, the pressure bearing margin of the downstream under the current operating conditions is calculated, serving as the disturbance pressure tolerance value. This value represents the pressure fluctuation range that the downstream load can withstand. Finally, combining the upper limit of the driving pressure and the disturbance pressure tolerance value, a pressure regulation safety boundary is defined, laying the foundation for subsequent... The pressure regulation is set within a safe range to prevent adjustments from exceeding the equipment's operational capacity. Then, a preset target pressure setpoint is obtained. The ratio of the upper limit of the driving pressure to the disturbance pressure tolerance is normalized under the constraint of the target pressure setpoint to obtain the outlet pressure dynamic balance coefficient. This coefficient integrates the driving capability of the high-pressure side and the downstream load disturbance characteristics, and is a core indicator for measuring the balance state of the mixer outlet pressure. Its value directly reflects the direction and magnitude of the outlet pressure adjustment required under the current operating conditions. Finally, a corresponding valve opening adjustment command is generated based on the outlet pressure dynamic balance coefficient and sent to the actuator of the high-pressure steam inlet valve. By controlling the valve opening, the high-pressure steam inlet flow is adjusted, thereby changing the driving capability of the high-pressure side, so that the actual pressure value at the mixer outlet gradually approaches the target pressure setpoint. For example, when the outlet pressure dynamic balance coefficient is low, it indicates that the high-pressure side driving capacity is insufficient to offset downstream load disturbances. In this case, an adjustment command to increase the valve opening is generated to increase the high-pressure steam intake, enhance the high-pressure side driving capacity, and thus raise the outlet pressure. When the outlet pressure dynamic balance coefficient is high, it indicates that the high-pressure side driving capacity is too strong, exceeding the load-bearing requirements of the downstream load. In this case, an adjustment command to decrease the valve opening is generated to reduce the high-pressure steam intake, reduce the high-pressure side driving capacity, and cause the outlet pressure to fall back to the target value. This step integrates the core quantitative coefficients of the high-pressure side and the downstream to generate a dynamic balance coefficient that reflects the outlet pressure balance state. Based on this, targeted valve opening adjustments are implemented, achieving dynamic and precise regulation of the outlet pressure. The quantitative analysis results of all previous steps are transformed into actual adjustment actions, completing the closed loop of the entire pressure stabilization regulation.

[0026] In one embodiment, step S2, which involves obtaining the dynamic response coefficient of the driving pressure based on the reference driving pressure and the high-pressure steam fluctuation data, includes: S21. Obtain historical pressure time series data of the high-pressure steam inlet within a preset historical time period, and obtain the pressure reference stable value of the high-pressure steam based on the historical pressure time series data, and use the pressure reference stable value as the reference driving pressure. S22. Obtain the real-time pressure value at the current moment based on the high-pressure steam inlet pressure data, and obtain the pressure transient deviation value based on the real-time pressure value and the reference driving pressure; S23. The pressure data at the high-pressure steam inlet is sampled within a unit time window to obtain a pressure instantaneous fluctuation sequence. The root mean square value of the fluctuation is calculated based on the pressure instantaneous fluctuation sequence, and the root mean square value of the fluctuation is used as the high-pressure steam fluctuation data. S24. Obtain the pressure response amplitude factor based on the pressure transient deviation value and the root mean square value of the fluctuation, and perform a fast Fourier transform on the pressure instantaneous fluctuation sequence to obtain the fluctuation spectrum energy distribution, and obtain the proportion of high-frequency fluctuation energy based on the fluctuation spectrum energy distribution. S25. Obtain the maximum value of the historical pressure response amplitude factor based on historical high-pressure steam inlet pressure data, and obtain the dynamic response coefficient of the driving pressure according to the pressure response amplitude factor and the proportion of high-frequency fluctuation energy. The driving pressure dynamic response coefficient characterizes the pressure recovery capability of the high-pressure steam source under a unit disturbance.

[0027] As described in steps S21-S25 above, this invention acquires historical pressure time-series data of the high-pressure steam inlet within a preset historical time period, and obtains the pressure benchmark stable value of the high-pressure steam based on the historical pressure time-series data. The pressure benchmark stable value is used as the benchmark driving pressure. This step determines the pressure benchmark state of the high-pressure steam inlet, providing a reference standard for subsequent pressure deviation and fluctuation analysis. The historical pressure time-series data of the high-pressure steam inlet is collected by a pressure sensor installed at the high-pressure steam inlet and stored in the equipment operation database. The preset historical time period can be set according to the actual operating conditions of the mixer, generally selecting 72 hours or 168 hours of stable equipment operation. By statistically analyzing the historical pressure time-series data within this time period, outliers are removed, and the mean or median pressure is calculated and determined as the pressure benchmark stable value and used as the benchmark driving pressure. The physical significance of this step lies in defining the normal stable state of the high-pressure steam inlet pressure, providing a quantitative reference for subsequent judgments on whether the pressure deviates from the normal state. For example, in an industrial heating scenario, by selecting 72 hours of historical pressure time-series data from stable mixer operation, and removing abnormal pressure values ​​caused by brief boiler malfunctions, the calculated average pressure is 0.8 MPa. This value is the benchmark driving pressure, which can then be used to determine whether there is a deviation in the real-time pressure of the high-pressure steam inlet. The technical effect of this step is that by determining the benchmark value through historical stable data, it avoids benchmark judgment deviations caused by instantaneous pressure fluctuations, ensuring the objectivity and rationality of the reference standard for subsequent deviation and fluctuation analysis.

[0028] The real-time pressure value is obtained based on the high-pressure steam inlet pressure data, and the transient pressure deviation value is obtained based on the real-time pressure value and the reference driving pressure. This step quantifies the instantaneous deviation of the high-pressure steam inlet pressure. The real-time pressure value of the high-pressure steam inlet is collected in real time by a pressure sensor at the high-pressure steam inlet. The collection frequency matches the operation monitoring requirements of the mixer, generally 1Hz-10Hz. The transient pressure deviation value is calculated by the difference between the current real-time pressure value and the reference driving pressure obtained in S21. A positive difference indicates that the real-time pressure is higher than the reference state, and a negative difference indicates that the real-time pressure is lower than the reference state. The physical significance of this step is to accurately capture the degree of deviation of the high-pressure steam inlet pressure from the stable reference state at the current moment, reflecting the transient change characteristics of the pressure. For example, if the reference driving pressure is 0.8MPa and the current real-time pressure value is 0.76MPa, the calculated transient pressure deviation value is -0.04MPa, indicating that the high-pressure steam inlet pressure is in a transient deviation below the reference state. The technical advantage of this step is that it enables real-time quantification of the transient deviation of the high-pressure steam inlet pressure, which can quickly capture instantaneous pressure changes and provide transient state basis for subsequent comprehensive analysis of pressure dynamic response characteristics.

[0029] The high-pressure steam inlet pressure data is sampled within a unit time window to obtain a pressure instantaneous fluctuation sequence. The root mean square value of the fluctuation is calculated based on the pressure instantaneous fluctuation sequence, and the root mean square value of the fluctuation is used as the high-pressure steam fluctuation data. This step quantifies the intensity of the high-pressure steam inlet pressure fluctuation. The unit time window can be set according to the characteristics of the pressure fluctuation, generally 5s-30s. Sliding sampling refers to extracting pressure data within a unit time window from the continuous high-pressure steam inlet pressure data with a fixed time step to form a continuous pressure instantaneous fluctuation sequence. The root mean square value of the fluctuation is obtained by squaring, averaging, and taking the square root of the difference between each data point in the pressure instantaneous fluctuation sequence and the sequence mean. The physical significance of this step lies in quantifying the intensity of pressure fluctuations at the high-pressure steam inlet over a short period. A larger root mean square (RMS) value indicates more severe instantaneous pressure fluctuations, and vice versa. For example, by selecting a 10-second time window for sliding sampling of the high-pressure steam inlet pressure data, the instantaneous pressure fluctuation sequence within a certain window is obtained as [0.79, 0.80, 0.78, 0.81, 0.79]. The calculated RMS value is 0.01 MPa, indicating that the instantaneous pressure fluctuation is relatively mild at this point. The technical advantage of this step is that through sliding sampling and RMS calculation, it achieves precise quantification of the intensity of pressure fluctuations. Compared to simple extreme value difference calculation, the RMS value can more comprehensively reflect the fluctuation characteristics of all data within the sequence, avoiding interference from a single extreme value in the fluctuation judgment.

[0030] The pressure response amplitude factor is obtained based on the pressure transient deviation value and the root mean square value of the fluctuation. A fast Fourier transform is then performed on the pressure transient fluctuation sequence to obtain the fluctuation spectrum energy distribution. The proportion of high-frequency fluctuation energy is then obtained based on the fluctuation spectrum energy distribution. This step involves the dual quantification of the amplitude response characteristics and frequency fluctuation characteristics of the high-pressure steam inlet pressure, and is a crucial link connecting the fundamental pressure characteristics and the dynamic response coefficient. The pressure response amplitude factor is calculated by normalizing and fusing the pressure transient deviation value and the root mean square value of the fluctuation. First, the two parameters are normalized to 0-1 respectively, and then... The influence of both factors on the pressure response characteristics is weighted and summed. The weights are set based on the degree of influence of pressure deviation and fluctuation on jet stability in industrial conditions. Generally, the weight of the transient pressure deviation value is 0.6, and the weight of the root mean square value of the fluctuation is 0.4. The fast Fourier transform is used to perform frequency domain transformation on the instantaneous pressure fluctuation sequence obtained in S23, converting the time-domain pressure fluctuation data into the frequency-domain spectral energy distribution. The frequency threshold of high-frequency fluctuations is set according to the operating characteristics of the mixer, generally above 0.1Hz. The proportion of high-frequency fluctuation energy is obtained by calculating the ratio of the energy value of the high-frequency band to the total spectral energy value. The physical significance of this step lies in the fact that the pressure response amplitude factor characterizes the amplitude response characteristics of the high-pressure steam inlet pressure under the combined action of deviation and fluctuation, while the high-frequency fluctuation energy proportion characterizes the energy proportion of the high-frequency components in the pressure fluctuation. High-frequency fluctuations have a greater impact on the stability of the high-pressure steam jet, and this proportion can reflect the potential influence of pressure fluctuations on the jet. For example, after normalizing the pressure transient deviation value, it is 0.2, and after normalizing the fluctuation root mean square value, it is 0.1. After weighted summation, the pressure response amplitude factor is 0.16. After performing a fast Fourier transform on the pressure instantaneous fluctuation sequence, the high-frequency band energy value is 0.02, the total spectrum energy value is 0.1, and the high-frequency fluctuation energy proportion is 20%, indicating that the pressure amplitude response characteristics are weak at this time, and the energy proportion of high-frequency fluctuations is low. The technical effect of this step is that it integrates pressure deviation and fluctuation characteristics through normalization fusion, and realizes the time-domain to frequency-domain conversion of pressure fluctuation through fast Fourier transform. For the first time, it incorporates the frequency characteristics of pressure into the high-pressure side state analysis, filling the gap in the existing technology for pressure frequency characteristic analysis, and providing a frequency dimension basis for subsequent accurate quantification of pressure dynamic response capability.

[0031] The maximum value of the historical pressure response amplitude factor is obtained based on historical high-pressure steam inlet pressure data. The dynamic response coefficient of the driving pressure is obtained based on the pressure response amplitude factor and the proportion of high-frequency fluctuation energy. The calculation formula is as follows: ; in, Indicates the dynamic response coefficient of the driving pressure. Indicates the pressure response amplitude factor. This represents the maximum value of the historical pressure response amplitude factor. This indicates the proportion of high-frequency fluctuation energy. express The weight value, express The weighting value is as follows: The dynamic response coefficient of the driving pressure is calculated by first comparing the current pressure response amplitude factor with the maximum value of the historical pressure response amplitude factor to obtain the normalized amplitude response coefficient. Then, the amplitude response coefficient is weighted and fused with the proportion of high-frequency fluctuation energy. The weighting weight is set according to the degree of influence of the two on the pressure recovery capability determined in industrial tests. Generally, the weight of the normalized amplitude response coefficient is 0.7, and the weight of the proportion of high-frequency fluctuation energy is 0.3. The final dynamic response coefficient of the driving pressure is a value between 0 and 1. This coefficient is the core quantitative indicator characterizing the pressure recovery capability of the high-pressure steam source under unit disturbance. The physical significance of this step lies in comprehensively integrating the amplitude response characteristics and frequency fluctuation characteristics of the high-pressure steam inlet pressure to form a single coefficient that fully reflects the dynamic response capability of the high-pressure steam source. The closer the coefficient value is to 1, the stronger the pressure recovery capability of the high-pressure steam source under a unit disturbance; the closer the coefficient value is to 0, the weaker the pressure recovery capability. For example, with a normalized amplitude response coefficient of 0.8 and a high-frequency fluctuation energy ratio of 0.2, the weighted fusion yields a driving pressure dynamic response coefficient of 0.62, indicating that the pressure recovery capability of the high-pressure steam source is at a moderate level. The technical effect of this step is that it integrates multi-dimensional pressure characteristic parameters into a single quantitative coefficient, achieving a precise and comprehensive evaluation of the dynamic response capability of the high-pressure steam source. This coefficient can be directly used as an input parameter for the subsequent calculation of the high-pressure side driving capability coefficient, providing a clear and quantifiable high-pressure side status basis for subsequent mixer outlet pressure regulation.

[0032] In one embodiment, step S3, which involves obtaining the sensitivity coefficient of the ejector structure based on the ejector end pressure value and the ejector flow rate data, includes: S31. Obtain the pressure sequence of the low-pressure steam inlet within a continuous time window, calculate the pressure change rate sequence based on the pressure sequence, and use the current value of the pressure sequence as the ejector end pressure value. S32. Obtain the geometric parameters of the mixer ejector cavity, and calculate the theoretical maximum ejector flow rate based on the geometric parameters and the ejector end pressure value, and use the theoretical maximum ejector flow rate as the reference ejector flow rate. S33. Obtain the real-time flow rate detection value of the low-pressure steam inlet, and obtain the flow rate deviation ratio based on the real-time flow rate detection value and the reference ejector flow rate; S34. Perform Kalman filtering on the pressure change rate sequence to obtain a smoothed pressure change rate, and obtain the flow resistance change gradient of the ejector cavity based on the smoothed pressure change rate and the flow deviation ratio. S35. Obtain the sensitivity coefficient of the ejector structure based on the flow resistance change gradient and the geometric parameters of the ejector cavity; The sensitivity coefficient of the ejector structure characterizes the degree of nonlinear response of the ejector cavity to flow rate under different pressure differences.

[0033] As described in steps S31-S35 above, existing technologies, when analyzing the ejector characteristics of the low-pressure side of a mixer, mostly rely on fixed geometric parameters or single flow and pressure detection values ​​for static judgment. The core problem with this approach is that it fails to dynamically capture the changing trend of the ejector end pressure, nor does it consider the dynamic changes in the flow resistance of the ejector cavity during actual operation. It cannot quantify the degree of nonlinear response of the ejector cavity to the flow rate under different pressure differentials. The static analysis results deviate from the actual dynamic operating state of the mixer, making it difficult to reflect the true operating characteristics of the low-pressure side ejector link, thus affecting the accuracy of subsequent pressure regulation. Therefore, this invention obtains the pressure sequence of the low-pressure steam inlet within a continuous time window, calculates the pressure change rate sequence based on the pressure sequence, and uses the current value of the pressure sequence as the ejector end pressure. The first step is to capture the pressure state and trend of the low-pressure steam ejector, providing core pressure data support for subsequent ejector characteristic analysis. The pressure sequence of the low-pressure steam inlet is continuously acquired by a pressure sensor installed at the ejector chamber of the mixer. The acquisition frequency is set according to the fluctuation characteristics of the low-pressure steam pipeline network, generally 1Hz-5Hz. The continuous time window is selected to reflect a reasonable duration that can reflect the dynamic changes in pressure, usually 30s-60s. The pressure change rate sequence is calculated by taking the difference between the pressure values ​​of two adjacent moments in the pressure sequence and dividing by the time interval, which intuitively reflects the change amplitude and trend of the ejector end pressure per unit time. The ejector end pressure value is directly extracted from the real-time detection value of the current moment in the pressure sequence, serving as the basic parameter for subsequent theoretical flow calculation. The physical significance of this step lies in accurately capturing the real-time status and dynamic trend of the ejector end pressure. The pressure change rate sequence reflects whether the pressure is rising, falling, or stable, providing a trend basis for subsequent analysis of the impact of pressure changes on ejector flow. For example, in a thermal system optimization scenario, the low-pressure steam inlet pressure sequence collected within a 60-second continuous time window is [0.20, 0.21, 0.20, 0.22, 0.23] MPa. The calculated pressure change rate sequence is [0.01, -0.01, 0.02, 0.01] MPa / s. The current ejector end pressure is 0.23 MPa, indicating that the ejector end pressure is continuously rising. The technical effect of this step is to achieve dynamic capture of the ejector end pressure status and trend. Compared to single real-time pressure detection, the pressure change rate sequence can reflect the dynamic trend of pressure in advance, laying a data foundation for subsequent dynamic analysis of ejector characteristics.

[0034] Obtain the geometric parameters of the mixer ejector cavity, and calculate the theoretical maximum ejector flow rate based on the geometric parameters and the ejector end pressure value. Use the theoretical maximum ejector flow rate as the benchmark ejector flow rate. This step quantifies the theoretical ejection capacity of low-pressure steam, providing a reference standard for subsequent actual flow rate deviation analysis. The geometric parameters of the mixer ejector cavity are inherent design parameters of the equipment, including the ejector cavity inlet diameter, flow channel length, contraction angle, expansion angle, etc., which can be directly obtained from the mixer's equipment design drawings and technical parameter manual. The theoretical maximum ejector flow rate is calculated based on Bernoulli's equation in fluid mechanics and the ejector flow rate calculation formula, combined with the geometric parameters of the ejector cavity and the ejector end pressure value. This value represents the maximum ejector flow rate that the ejector cavity can achieve under ideal flow channel conditions at the current ejector end pressure. Using this as the benchmark ejector flow rate is the core reference for measuring whether the actual ejector flow rate is reasonable. The physical significance of this step lies in defining the theoretical maximum ejection capacity of low-pressure steam under the current ejector end pressure. By combining the calculation method based on the inherent geometric parameters of the equipment, the baseline ejection flow rate is matched with the actual structure of the mixer, avoiding calculation deviations caused by general flow formulas. For example, if the inlet diameter of the ejector chamber is 50mm, the contraction angle is 15°, and the current ejector end pressure is 0.23MPa, the theoretical maximum ejection flow rate calculated using fluid dynamics formulas is 200kg / h. This value is the baseline ejection flow rate, representing the ideal maximum ejection capacity of the ejector chamber at this time. The technical effect of this step is that it achieves accurate calculation of the theoretical ejection flow rate by combining the inherent geometric parameters of the equipment, providing a reference standard that matches the actual equipment for subsequent flow deviation analysis, thus improving the objectivity and rationality of the analysis results.

[0035] The real-time flow rate of the low-pressure steam inlet is obtained, and the flow deviation ratio is calculated based on the real-time flow rate and the reference ejector flow rate. This step quantifies the degree of deviation between the actual ejector flow rate and the theoretical ejector flow rate, and intuitively reflects the difference between the actual ejection effect of the ejector cavity and the ideal state. The real-time flow rate of the low-pressure steam inlet is collected in real time by a flow sensor installed on the low-pressure steam inlet pipeline. The collection frequency is consistent with that of the pressure sensor to ensure the time synchronization of pressure and flow data. The flow deviation ratio is calculated by comparing the real-time flow rate with the reference ejector flow rate. A ratio greater than 1 indicates that the actual ejector flow rate exceeds the theoretical maximum ejector flow rate, which is mostly caused by measurement error or instantaneous pipeline fluctuations. A ratio less than 1 indicates that the actual ejector flow rate has not reached the theoretical value, reflecting problems such as flow resistance loss in the ejector cavity. The physical significance of this step lies in quantifying the actual ejection efficiency of the ejector cavity under the current operating conditions. The magnitude of the flow deviation ratio directly reflects the degree of deviation between the actual ejection flow rate and the theoretical value. The greater the deviation, the greater the difference between the actual flow channel state of the ejector cavity and the ideal state. For example, if the baseline ejection flow rate is 200 kg / h and the real-time flow rate is 160 kg / h, the calculated flow deviation ratio is 0.8, indicating that the actual ejection flow rate only reaches 80% of the theoretical maximum ejection flow rate, and the actual ejection efficiency of the ejector cavity is significantly insufficient. The technical effect of this step is to achieve precise quantification of the deviation of the actual ejection flow rate, transforming the ejection effect into a numerical indicator that can be directly compared and analyzed, providing an intuitive basis for the deviation in subsequent analysis of changes in the flow resistance of the ejector cavity.

[0036] Kalman filtering is applied to the pressure change rate sequence to obtain a smoothed pressure change rate. The flow resistance gradient of the ejector cavity is then obtained based on the smoothed pressure change rate and the flow deviation ratio. This step is the core quantification of the pressure change rate noise reduction optimization and dynamic flow resistance change, and is a crucial link connecting pressure, flow characteristics, and ejector structure characteristics. The Kalman filtering algorithm uses a standard linear Kalman filter model, with the pressure change rate sequence as the observed value. The process noise covariance is set to 0.001 and the observation noise covariance to 0.005. Through prediction and updating iterations… The process eliminates random measurement noise in the pressure change rate sequence to obtain a smoothed pressure change rate, making the pressure change trend more consistent with the actual situation. The flow resistance change gradient is calculated by normalizing and fusing the smoothed pressure change rate and the flow deviation ratio. First, the two parameters are normalized to 0-1 respectively, and then weights are set according to their influence on the flow resistance change. The weight of the smoothed pressure change rate is 0.55, and the weight of the flow deviation ratio is 0.45. The weighted sum is used to obtain the flow resistance change gradient, which reflects the dynamic amplitude of the ejector cavity flow resistance with pressure change. The physical significance of this step lies in the fact that Kalman filtering effectively eliminates noise interference in the pressure change rate sequence, preventing spurious pressure change signals from affecting subsequent analysis. Meanwhile, the flow resistance change gradient precisely quantifies the dynamic characteristics of the ejector cavity flow resistance as the ejector end pressure changes. A larger gradient value indicates a more significant impact of pressure change on flow resistance and a more unstable flow channel characteristic of the ejector cavity. For example, after Kalman filtering, the smoothed pressure change rate is 0.015 MPa / s, and the normalized flow deviation ratio is 0.2. The weighted fusion calculation yields a flow resistance change gradient of 0.1825, indicating that the pressure increase has a certain impact on the flow resistance, and the ejector cavity flow resistance shows a slight upward trend. The technical effect of this step is that Kalman filtering achieves noise reduction and optimization of the pressure change rate data, improving data reliability. Simultaneously, it integrates the pressure change trend and the degree of flow deviation into a flow resistance change gradient, achieving for the first time a quantitative analysis of the dynamic changes in ejector cavity flow resistance. This fills the gap in existing technology for analyzing the dynamic characteristics of ejector cavity flow resistance and provides a core flow resistance basis for subsequent precise quantification of the ejector structure sensitivity coefficient.

[0037] The ejector structure sensitivity coefficient is obtained based on the flow resistance change gradient and the geometric parameters of the ejector cavity. This step is the final quantification of the nonlinear response characteristics of the ejector cavity, realizing the fusion of dynamic flow resistance changes and inherent structural characteristics of the equipment. The ejector structure sensitivity coefficient is calculated as follows: First, the geometric parameters of the ejector cavity are normalized, and the inlet diameter and contraction angle of the ejector cavity are selected as the core structural parameters. According to their influence weight on the ejection characteristics, the inlet diameter weight is set to 0.6 and the contraction angle weight is set to 0.4. The normalized value of the structural parameters is calculated. Then, the normalized value of the structural parameters is weighted and fused with the flow resistance change gradient obtained in S34. The weight of the flow resistance change gradient is 0.5 and the weight of the normalized value of the structural parameters is 0.5. The final ejector structure sensitivity coefficient is a value between 0 and 1. This coefficient is the core quantitative index characterizing the degree of nonlinear response of the ejector cavity to the flow rate under different pressure differences. The physical significance of this step lies in comprehensively integrating the dynamic changes in flow resistance and the inherent geometric characteristics of the ejector cavity to form a single coefficient that fully reflects the nonlinear response characteristics of the ejector structure. The closer the coefficient value is to 1, the more sensitive the flow rate of the ejector cavity is to changes in pressure difference; the closer the coefficient value is to 0, the more sluggish the response. For example, with a normalized structural parameter value of 0.7 and a flow resistance gradient of 0.1825, the weighted fusion yields an ejector structure sensitivity coefficient of 0.44125, indicating that the flow rate of the ejector cavity is moderately sensitive to changes in pressure difference, and the impact of pressure changes on the ejector flow rate is relatively mild. The technical effect of this step is that it integrates the dynamic changes in flow resistance and the inherent structural characteristics of the equipment into a single quantitative coefficient, achieving a precise and comprehensive evaluation of the nonlinear response characteristics of the ejector cavity. This coefficient can be directly used as an input parameter for the subsequent calculation of the high-pressure side drive capability coefficient, providing a clear and quantifiable basis for the low-pressure side status for subsequent mixer outlet pressure regulation.

[0038] In one embodiment, step S4, which involves obtaining the high-pressure side drive capability coefficient based on the dynamic response coefficient of the drive pressure and the sensitivity coefficient of the ejector structure, includes: S41. Obtain the nozzle throat area parameters and nozzle outlet area parameters of the high-pressure steam inlet, and calculate the nozzle expansion ratio based on the nozzle throat area parameters and the nozzle outlet area parameters. S42. Obtain the jet flow correction factor of high-pressure steam based on the driving pressure dynamic response coefficient and the expansion ratio; S43. Obtain the momentum exchange efficiency coefficient of the mixing chamber based on the sensitivity coefficient of the ejector structure and the ejector momentum correction factor; S44. Obtain the high-pressure side driving capability coefficient based on the momentum exchange efficiency coefficient and the real-time pressure value of the high-pressure steam inlet, wherein the high-pressure side driving capability coefficient characterizes the actual entrainment capability of the high-pressure steam jet on the low-pressure steam in the mixing chamber.

[0039] As described in steps S41-S44 above, this invention obtains the nozzle throat area parameters and nozzle outlet area parameters of the high-pressure steam inlet, and calculates the nozzle expansion ratio based on the nozzle throat area parameters and nozzle outlet area parameters. This step quantifies the core geometric jet characteristics of the high-pressure steam inlet nozzle, providing a basic structural parameter basis for the subsequent calculation and correction of jet momentum. The nozzle throat area parameters and nozzle outlet area parameters of the high-pressure steam inlet are inherent design structural parameters of the mixer, which can be directly obtained from the mixer's equipment design drawings, technical parameter manuals, and equipment factory data. The nozzle expansion ratio is calculated by the ratio of the nozzle outlet area to the nozzle throat area. This value is a core geometric index reflecting the expansion characteristics of high-pressure steam when passing through the nozzle, and directly determines the acceleration process of high-pressure steam in the nozzle and the momentum state of the jet outlet. The physical significance of this step lies in transforming the core geometric structural features of the nozzle into quantifiable jet expansion indicators, clarifying the fundamental impact of the nozzle structure on the high-pressure steam jet momentum. For example, if the nozzle throat area is 200 mm² and the nozzle outlet area is 300 mm² obtained from equipment data, the calculated nozzle expansion ratio is 1.5, indicating that high-pressure steam will undergo a certain degree of expansion and acceleration when passing through the nozzle, and the jet momentum will change accordingly due to the nozzle's structural features. The technical effect of this step is to accurately extract and quantify the core jet structural parameters of the nozzle, laying a solid geometric foundation for subsequent correction of jet momentum based on actual operating conditions, ensuring that subsequent momentum calculations are no longer divorced from the actual jet characteristics of the nozzle.

[0040] The jet flow correction factor for high-pressure steam is obtained based on the driving pressure dynamic response coefficient and the expansion ratio. This step corrects the theoretical jet flow of high-pressure steam under actual operating conditions, realizing the fusion of the dynamic response characteristics of the high-pressure side and the nozzle structural characteristics. The driving pressure dynamic response coefficient is a quantitative index calculated in S25 that characterizes the pressure recovery capability of the high-pressure steam source under unit disturbance. The jet flow correction factor is calculated by normalizing and fusing the driving pressure dynamic response coefficient and the nozzle expansion ratio. First, the two parameters are normalized to 0-1 respectively. Then, weights are set according to the actual influence of the two on the high-pressure steam jet flow. Combining the influence ratio of the nozzle structure and the dynamic characteristics of the steam source on the jet flow in industrial tests, the weight of the nozzle expansion ratio is set to 0.45 and the weight of the driving pressure dynamic response coefficient is set to 0.55. The final jet flow correction factor is obtained by weighted summation. This factor is a value between 0 and 1 and is used to correct the high-pressure steam jet flow calculated based on ideal conditions. The physical significance of this step lies in combining the actual dynamic response capability of the high-pressure steam source with the structural expansion characteristics of the nozzle to adjust the theoretical jet flux to better match actual operating conditions. The closer the correction factor is to 1, the closer the actual jet flux of the high-pressure steam is to the theoretical value; conversely, the greater the deviation, the closer the actual jet flux is to the theoretical value. For example, if the driving pressure dynamic response coefficient is 0.62 (normalized to 0.62) and the nozzle expansion ratio is 1.5 (normalized to 0.75), the weighted summation yields a jet flux correction factor of 0.6785. This indicates that the theoretical jet flux of the high-pressure steam needs to be corrected according to this factor to obtain a jet flux value that closely matches actual operating conditions. The technical effect of this step is that it integrates the dynamic response characteristics of the high-pressure steam source with the structural characteristics of the nozzle for the first time, achieving actual operating condition correction of the theoretical jet flux. This avoids the problem of decoupling from actual operating conditions caused by relying solely on nozzle structural parameters to calculate the jet flux, thus improving the accuracy of jet flux calculation.

[0041] The momentum exchange efficiency coefficient of the mixing chamber is obtained based on the ejector structure sensitivity coefficient and the jet momentum correction factor. This step quantifies the momentum exchange effect between the high-pressure steam jet and the low-pressure steam in the mixing chamber, realizing the coupled analysis of the actual jet characteristics on the high-pressure side and the ejector structure characteristics on the low-pressure side. The ejector structure sensitivity coefficient is a quantitative index calculated in S35 that characterizes the nonlinear response of the ejector cavity to the flow rate under different pressure differences. The momentum exchange efficiency coefficient is obtained by normalizing and fusing the ejector structure sensitivity coefficient and the jet momentum correction factor. First, the two parameters are normalized to 0-1 respectively. Then, based on the influence of the high-pressure side jet flow and the low-pressure side ejector structure on the momentum exchange effect under industrial conditions, the weight of the jet momentum correction factor is set to 0.6 and the weight of the ejector structure sensitivity coefficient is set to 0.4. The final momentum exchange efficiency coefficient is obtained by weighted summation. This coefficient is a value between 0 and 1, which directly reflects the effective degree of momentum transfer from the high-pressure steam jet to the low-pressure steam in the mixing chamber. The physical significance of this step lies in quantifying the actual momentum exchange effect between the high-pressure side jet and the low-pressure side steam in the mixing chamber. It considers the influence of the response characteristics of the low-pressure side ejector structure on momentum transfer. The closer the coefficient is to 1, the higher the momentum exchange efficiency, and the more effectively the momentum of the high-pressure steam jet can drive the low-pressure steam. Conversely, there is a loss in momentum exchange. For example, the jet momentum correction factor is 0.6785, which is 0.6785 after normalization, and the ejector structure sensitivity coefficient is 0.44125, which is 0.44125 after normalization. After weighted summation, the momentum exchange efficiency coefficient is 0.58365, indicating that there is a certain loss in the momentum exchange between the high-pressure steam jet and the low-pressure steam in the mixing chamber, and the effective utilization of the jet momentum is at a moderate level. The technical effect of this step is that it realizes the coupled analysis of the operating characteristics of the high-pressure side and the low-pressure side, incorporates the response characteristics of the low-pressure side ejector structure into the analysis system of the high-pressure side driving capability, fills the gap in the existing technology that ignores the coupling effect of the high and low pressure sides, and makes the analysis of momentum exchange efficiency more in line with the actual operating state of the mixer.

[0042] The high-pressure side driving capability coefficient is obtained based on the momentum exchange efficiency coefficient and the real-time pressure value at the high-pressure steam inlet. This step is the final comprehensive quantification of the actual driving capability of the high-pressure steam side, and it integrates the results of all previous high-pressure side, nozzle, and low-pressure side characteristic analyses. The momentum exchange efficiency coefficient is the quantified index calculated in S43. The real-time pressure value at the high-pressure steam inlet is collected in real time by a pressure sensor installed at the high-pressure steam inlet. The collection frequency matches the mixer's operation monitoring requirements to ensure data real-time performance. The high-pressure side driving capability coefficient is calculated by first... The real-time pressure value at the inlet is normalized to 0-1 according to the rated pressure of the equipment to obtain a normalized real-time pressure value. Then, the normalized real-time pressure value is weighted and fused with the momentum exchange efficiency coefficient. Considering the influence of real-time pressure and momentum exchange efficiency on the actual driving capability of the high-pressure side, the weight of the normalized real-time pressure value is set to 0.55 and the weight of the momentum exchange efficiency coefficient is set to 0.45. After weighted summation, the final high-pressure side driving capability coefficient is obtained. This coefficient is a value between 0 and 1 and is the core quantitative indicator characterizing the actual entrainment capability of the high-pressure steam jet on low-pressure steam in the mixing chamber. The physical significance of this step lies in comprehensively integrating the real-time pressure state of high-pressure steam and the momentum exchange efficiency between the jet and low-pressure steam to form a single quantitative coefficient that can fully reflect the actual entrainment capacity of the high-pressure side. The closer the coefficient is to 1, the stronger the actual entrainment capacity of the high-pressure steam on the low-pressure steam, and the more sufficient the driving capacity of the high-pressure side of the mixer. Conversely, the driving capacity is insufficient. For example, the rated pressure of the high-pressure steam inlet is 1.0 MPa, the real-time pressure is 0.8 MPa, and after normalization it is 0.8. The momentum exchange efficiency coefficient is 0.58365. After weighted summation, the high-pressure side driving capacity coefficient is 0.6926425, indicating that the actual driving capacity of the high-pressure side of the mixer is at a medium level at this time. It can provide a certain entrainment power for ejector mixing, but it has not yet reached the optimal state. The technical effect of this step is that it integrates the multi-dimensional high and low pressure side and nozzle structural features into a single high-pressure side driving capability coefficient, realizing accurate and comprehensive quantification of the actual entrainment capacity of high-pressure steam. This coefficient can be directly used as the core input parameter for subsequent dynamic balance adjustment of outlet pressure, providing a clear and quantifiable basis for the high-pressure side status for subsequent pressure regulation, making the analysis of outlet pressure regulation more targeted.

[0043] In one embodiment, step S5, which involves obtaining a real-time outlet pressure sequence and a pressure fluctuation spectrum based on the actual outlet pressure value, and obtaining a downstream load disturbance coefficient based on the real-time outlet pressure sequence and the pressure fluctuation spectrum, includes: S51. The actual value of the outlet pressure is continuously collected at a preset sampling frequency to obtain the real-time outlet pressure sequence. S52. Perform empirical mode decomposition on the real-time outlet pressure sequence to obtain multiple intrinsic mode function components, and take the intrinsic mode function components with frequencies higher than the preset cutoff frequency as high-frequency pressure fluctuation components. S53. Perform Hilbert transform on the high-frequency pressure fluctuation components to obtain the instantaneous pressure fluctuation amplitude sequence and the instantaneous pressure fluctuation frequency sequence; S54. Calculate the cumulative value of pressure fluctuation energy per unit time based on the instantaneous pressure fluctuation amplitude sequence, and calculate the main frequency offset of pressure fluctuation based on the instantaneous pressure fluctuation frequency sequence. S55. Obtain the downstream load disturbance coefficient based on the accumulated value of the pressure fluctuation energy and the main frequency offset of the pressure fluctuation, wherein the downstream load disturbance coefficient characterizes the reaction strength of the downstream steam-using equipment on the mixer outlet pressure.

[0044] As described in steps S51-S55 above, the present invention continuously collects the actual value of the outlet pressure at a preset sampling frequency to obtain the real-time outlet pressure sequence. This step is the basic data collection link for the analysis of the fluctuation characteristics of the mixer outlet pressure, providing continuous and real pressure time-series data for all subsequent signal processing and feature analysis. The actual value of the outlet pressure is detected and acquired in real time by a high-precision pressure sensor installed at the outlet of the steam jet mixer. The detection accuracy of the sensor matches the pressure regulation accuracy requirements of the mixer, which is generally 0.001MPa. The preset sampling frequency is set according to the fluctuation characteristics of the downstream load disturbance. Combined with the common frequency range of load disturbance in industrial conditions, the sampling frequency is set to 2Hz-5Hz, which can not only fully capture the high-frequency fluctuation characteristics of the pressure, but also avoid data redundancy due to excessively high sampling frequency. The real-time outlet pressure sequence is a one-dimensional time-series data formed by arranging the continuously collected actual values ​​of the outlet pressure in chronological order, which contains all the fluctuation information of the outlet pressure in the time dimension. The physical significance of this step lies in transforming the continuous physical change process of the mixer outlet pressure into a digitally processable time-series data sequence, achieving a complete record and digital representation of the outlet pressure fluctuation state. For example, in an industrial heating scenario, by continuously acquiring the actual outlet pressure value at a sampling frequency of 3Hz, a real-time outlet pressure sequence for a certain period is obtained as [0.30, 0.31, 0.29, 0.32, 0.30, 0.28] MPa. This sequence completely records the up-and-down fluctuations of the outlet pressure during that period. The technical effect of this step is that, through standardized continuous sampling, time-series data containing all the fluctuation information of the outlet pressure is obtained, laying a solid data foundation for subsequent refined signal processing. Compared with discrete pressure sampling, continuous time-series sequences can more comprehensively reflect the fluctuation characteristics of the outlet pressure.

[0045] Empirical Mode Decomposition (EMD) is performed on the real-time outlet pressure sequence to obtain multiple intrinsic mode function (IMF) components. IMF components with frequencies higher than a preset cutoff frequency are identified as high-frequency pressure fluctuation components. This step involves frequency-domain hierarchical processing of the real-time outlet pressure sequence, achieving frequency separation of the pressure fluctuation signal. The EMD algorithm is employed, which decomposes the real-time outlet pressure sequence into multiple IMF components with different time scales and a residual component through multiple screenings. Each IMF component corresponds to a fluctuation signal within a certain frequency range in the outlet pressure sequence, while the residual component represents the trend term of the sequence. The preset cutoff frequency is set based on the operating characteristics of the steam jet mixer and the frequency characteristics of downstream load disturbances. Combining industrial test data, the preset cutoff frequency is set to 0.1Hz, which is the critical frequency for distinguishing between slow changes and sudden changes in downstream load. The high-frequency pressure fluctuation component is the set of all IMF components with frequencies higher than 0.1Hz, corresponding to rapid pressure fluctuations caused by sudden changes in downstream load. The physical significance of this step lies in decomposing the complex outlet pressure fluctuation signal into single fluctuation components of different frequencies, achieving precise separation of high-frequency pressure fluctuation signals. High-frequency pressure fluctuations are the main form of disturbance to outlet pressure caused by sudden changes in downstream load. Extracting them separately makes subsequent disturbance characteristic analysis more targeted. For example, after performing empirical mode decomposition on the real-time outlet pressure sequence, five intrinsic mode function components are obtained. The frequencies of the first two components are 0.2Hz and 0.15Hz, respectively, both higher than the preset cutoff frequency of 0.1Hz. These two components constitute the high-frequency pressure fluctuation components, representing the pressure disturbance signal caused by sudden changes in downstream load. The technical effect of this step is that it achieves frequency domain layering of the pressure fluctuation signal through empirical mode decomposition, separating the outlet pressure fluctuation signal according to frequency characteristics for the first time, accurately extracting the high-frequency pressure fluctuation components that reflect sudden changes in downstream load, avoiding interference from low-frequency fluctuation signals in load disturbance characteristic analysis, and improving the targeting and accuracy of subsequent analysis.

[0046] The high-frequency pressure fluctuation components are subjected to Hilbert transform to obtain the instantaneous pressure fluctuation amplitude sequence and the instantaneous pressure fluctuation frequency sequence. This step extracts the instantaneous features of the high-frequency pressure fluctuation components, realizing the time-based representation of the pressure fluctuation amplitude and frequency. The Hilbert transform uses a standard complex function transform algorithm to analytically extend the extracted high-frequency pressure fluctuation components, constructing the corresponding analytical signal. The instantaneous pressure fluctuation amplitude sequence is obtained by taking the modulus of the analytical signal. This sequence reflects the real-time change of the amplitude of the high-frequency pressure fluctuation in the time dimension. The instantaneous pressure fluctuation frequency sequence is obtained by differentiating the amplitude of the analytical signal. This sequence reflects the real-time change of the frequency of the high-frequency pressure fluctuation in the time dimension. The physical significance of this step lies in transforming the high-frequency pressure fluctuation component from frequency domain characteristics to instantaneous amplitude and frequency characteristics in the time dimension, thereby realizing the dynamic capture of downstream load disturbances. The instantaneous pressure fluctuation amplitude sequence can reflect the intensity change of the load disturbance, and the instantaneous pressure fluctuation frequency sequence can reflect the frequency change of the load disturbance. For example, after performing a Hilbert transform on the high-frequency pressure fluctuation component, the instantaneous pressure fluctuation amplitude sequence is [0.01, 0.02, 0.015, 0.025, 0.018] MPa, and the instantaneous pressure fluctuation frequency sequence is [0.2, 0.2, 0.18, 0.22, 0.19] Hz. This result indicates that the intensity of the downstream load disturbance has slightly increased, while the frequency fluctuates slightly between 0.18 Hz and 0.22 Hz. The technical effect of this step is that it achieves accurate extraction of the instantaneous characteristics of high-frequency pressure fluctuation components through Hilbert transform, transforming the original frequency domain signal into a time-series feature sequence that can reflect real-time changes. This fills the gap in existing technologies that cannot capture the dynamic characteristics of load disturbances, and provides core data for subsequent quantification of the energy and frequency offset characteristics of load disturbances.

[0047] The cumulative pressure fluctuation energy per unit time is calculated based on the instantaneous pressure fluctuation amplitude sequence, and the dominant frequency offset of the pressure fluctuation is calculated based on the instantaneous pressure fluctuation frequency sequence. This step quantifies the energy intensity and frequency characteristics of the downstream load disturbance, realizing the transformation from a fluctuation characteristic sequence to a disturbance quantification index. The calculation of the cumulative pressure fluctuation energy is based on the basic formula of fluctuation energy. Each value in the instantaneous pressure fluctuation amplitude sequence is squared, summed, and then divided by the sampling time to obtain the cumulative energy per unit time. The unit of this value is MPa² / s. The larger the value, the higher the frequency of the pressure wave. The stronger the energy of the kinetic energy, the greater the intensity of the downstream load disturbance. The main frequency offset of the pressure fluctuation is first calculated by statistically analyzing the instantaneous pressure fluctuation frequency sequence to obtain the main frequency value of the sequence, that is, the frequency value with the highest frequency. Then, the difference between this main frequency value and the reference main frequency value of the high-frequency fluctuation of the outlet pressure during stable operation of the mixer is calculated to obtain the main frequency offset. The reference main frequency value is obtained by statistically analyzing the historical operating data of the mixer when there is no obvious load disturbance, and is generally 0.1Hz. The unit of the main frequency offset is Hz. The larger the absolute value, the more obvious the pressure fluctuation frequency offset caused by the downstream load disturbance. The physical significance of this step lies in transforming the amplitude and frequency characteristics of instantaneous pressure fluctuations into directly quantifiable energy and frequency shift indicators. These two indicators characterize the core features of downstream load disturbances from the two dimensions of energy intensity and frequency change, respectively. For example, with the sum of squares of the instantaneous pressure fluctuation amplitude sequence being 0.001565 MPa² and a sampling time of 5 seconds, the calculated cumulative energy of the pressure fluctuation per unit time is 0.000313 MPa² / s, and the dominant frequency of the instantaneous pressure fluctuation frequency sequence is 0.2 Hz. The difference between this and the reference dominant frequency of 0.1 Hz is 0.1 Hz, meaning the dominant frequency shift of the pressure fluctuation is 0.1 Hz. This result indicates that the downstream load disturbance has a certain energy intensity, causing a significant shift in the dominant frequency of the pressure fluctuation. The technical effect of this step is that, through standardized calculation methods, the abstract instantaneous characteristics of pressure fluctuations are transformed into specific and comparable quantitative indicators, achieving accurate quantification of the energy intensity and frequency shift characteristics of downstream load disturbances. This provides two core quantitative bases for subsequent fusion calculation of the downstream load disturbance coefficient.

[0048] The downstream load disturbance coefficient is obtained based on the accumulated pressure fluctuation energy and the dominant frequency offset of the pressure fluctuation. This step is the final comprehensive quantification of the downstream load disturbance characteristics, realizing the fusion of disturbance energy and frequency offset characteristics. The calculation method of the downstream load disturbance coefficient is as follows: first, the accumulated pressure fluctuation energy and the dominant frequency offset of the pressure fluctuation are normalized to 0-1 to eliminate the difference in the dimensions of the two indicators. Then, weights are set according to the influence of the two indicators on the degree of downstream load disturbance in industrial conditions. Combined with the analysis of a large amount of industrial test data and actual operation cases, the accumulated pressure fluctuation energy reflects the actual intensity of the load disturbance, and the weight is set to 0.6. The dominant frequency offset of the pressure fluctuation reflects the abnormality of the load disturbance, and the weight is set to 0.4. The two normalized indicators are multiplied by their corresponding weights and then summed to obtain the final downstream load disturbance coefficient. This coefficient is a value between 0 and 1 and is the core quantitative indicator characterizing the intensity of the reaction force of the downstream steam-using equipment on the mixer outlet pressure. The physical significance of this step lies in comprehensively integrating the energy intensity and frequency offset characteristics of downstream load disturbances to form a single quantitative coefficient that fully reflects the degree of downstream load disturbance. The closer the coefficient value is to 1, the greater the reaction strength of the downstream load on the outlet pressure, and the more significant the impact of downstream load disturbance on the mixer outlet pressure. Conversely, the smaller the disturbance impact, the less significant the reaction. For example, if the normalized cumulative energy value of pressure fluctuation is 0.6 and the normalized main frequency offset of pressure fluctuation is 0.8, the weighted summation yields a downstream load disturbance coefficient of 0.68, indicating that the downstream load exerts a moderate disturbance on the mixer outlet pressure, and the impact of this disturbance needs to be fully considered in the outlet pressure adjustment. The technical effect of this step is that it integrates two different dimensions of load disturbance quantitative indicators into a single downstream load disturbance coefficient, achieving a comprehensive and accurate characterization of the degree of downstream load disturbance. This coefficient can be directly used as the core input parameter for the subsequent calculation of the outlet pressure dynamic balance coefficient, providing a clear and quantifiable downstream state basis for subsequent precise adjustment of the outlet pressure.

[0049] In one embodiment, step S6, which involves obtaining the outlet pressure dynamic balance coefficient based on the high-pressure side drive capability coefficient and the downstream load disturbance coefficient, and adjusting the outlet pressure of the steam jet mixer based on the outlet pressure dynamic balance coefficient, includes: S61. Obtain the theoretical maximum output pressure of the high-pressure side under the current operating conditions based on the high-pressure side driving capability coefficient, and use the theoretical maximum output pressure as the upper limit value of the driving pressure. S62. Obtain the downstream pressure bearing margin under the current operating conditions based on the downstream load disturbance coefficient, and use the pressure bearing margin as the disturbance pressure tolerance value. S63. Obtain the pressure regulation safety boundary based on the upper limit value of the driving pressure and the disturbance pressure tolerance value; S64. Obtain a preset target pressure setting value, and obtain an outlet pressure dynamic balance coefficient based on the pressure adjustment safety boundary and the target pressure setting value, wherein the outlet pressure dynamic balance coefficient is a normalized value of the ratio of the upper limit of the driving pressure to the disturbance pressure tolerance value under the constraint of the target pressure setting value. S65. Generate a valve opening adjustment command based on the outlet pressure dynamic balance coefficient, and control the opening of the high-pressure steam inlet valve based on the valve opening adjustment command, so that the actual pressure value at the mixer outlet approaches the target pressure setting value.

[0050] As described in steps S61-S65 above, the present invention obtains the theoretical maximum output pressure of the high-pressure side under the current operating conditions based on the high-pressure side driving capability coefficient, and uses the theoretical maximum output pressure as the upper limit of the driving pressure. This step defines the upper limit of the pressure output capability of the high-pressure side under the current operating conditions, and sets the capability boundary of the high-pressure side for subsequent pressure regulation. The high-pressure side driving capability coefficient is the core quantitative indicator calculated in S44, which characterizes the actual entrainment capability of the high-pressure steam jet on the low-pressure steam in the mixing chamber. The theoretical maximum output pressure is calculated by multiplying the high-pressure side driving capability coefficient with the rated maximum output pressure of the high-pressure side of the mixer. The rated maximum output pressure of the high-pressure side of the mixer is an inherent design parameter of the equipment, which can be directly obtained from the technical parameter manual of the mixer and the equipment factory data. The upper limit of the driving pressure is the maximum pressure support that the high-pressure side can provide to the mixer under the current operating conditions, and is the upper limit of the pressure that the high-pressure side can reach during the pressure regulation process. The physical significance of this step lies in dynamically defining the upper limit of pressure output under current operating conditions based on the actual driving capacity of the high-pressure side. This prevents regulation failure caused by exceeding the actual capacity range of the high-pressure side during pressure adjustment. For example, if the rated maximum output pressure of the high-pressure side of the mixer is 0.5 MPa, and the currently calculated driving capacity coefficient of the high-pressure side is 0.7, the theoretical maximum output pressure obtained through multiplication is 0.35 MPa. This value is the upper limit of the driving pressure, indicating that the high-pressure side can provide a maximum of 0.35 MPa of pressure support to the mixer under current operating conditions. The technical effect of this step is that it achieves dynamic definition of the upper limit of the driving pressure on the high-pressure side. Compared with the traditional fixed pressure upper limit, this value can change in real time according to the actual operating status of the high-pressure side, allowing the upper limit of pressure regulation to be more closely aligned with the actual operating capacity of the equipment, thus avoiding the problem of over-capacity regulation from the source.

[0051] The downstream pressure bearing margin under the current operating condition is obtained based on the downstream load disturbance coefficient, and the pressure bearing margin is used as the disturbance pressure tolerance value. This step is a quantitative definition of the pressure fluctuation range that the downstream load can withstand under the current disturbance state, setting the downstream tolerance boundary for subsequent pressure regulation. The downstream load disturbance coefficient is a quantitative index calculated in S55 that characterizes the reaction strength of the downstream steam-using equipment on the mixer outlet pressure. The pressure bearing margin is calculated by multiplying the rated fluctuation margin of the mixer outlet pressure by (1-downstream load disturbance coefficient). The rated fluctuation margin of the mixer outlet pressure is an inherent parameter set by the equipment according to the downstream steam demand, representing the maximum pressure fluctuation range that the downstream load can withstand without significant disturbance. It can be obtained from the mixer's operation configuration file. The disturbance pressure tolerance value is the upper limit of the pressure fluctuation that the downstream load can withstand under the current operating condition, which is the pressure fluctuation boundary that needs to be controlled during the pressure regulation process. The physical significance of this step lies in dynamically defining the pressure tolerance margin of the downstream load under the current operating conditions based on the actual disturbance intensity of the downstream load. This prevents the pressure regulation process from exceeding the tolerance range of the downstream load, which could lead to abnormal operation of the steam-using equipment. For example, if the rated fluctuation margin of the mixer outlet pressure is 0.08 MPa, and the currently calculated downstream load disturbance coefficient is 0.68, the pressure tolerance margin obtained by multiplying (1-0.68) by 0.08 is 0.0256 MPa. This value is the disturbance pressure tolerance value, indicating that the downstream load can only withstand a pressure fluctuation of 0.0256 MPa under the current disturbance state. The technical effect of this step is that it achieves dynamic definition of the downstream disturbance pressure tolerance value. Compared with the traditional fixed pressure fluctuation threshold, this value can change in real time according to the actual disturbance intensity of the downstream load, making the lower limit of pressure regulation more closely match the actual operating state of the downstream steam-using equipment, thus avoiding equipment operation problems caused by pressure fluctuations exceeding the downstream tolerance range.

[0052] The pressure regulation safety boundary is obtained based on the upper limit of the driving pressure and the disturbance pressure tolerance value. This step is a comprehensive definition of the mixer outlet pressure regulation range, which integrates the capacity boundary of the high-pressure side and the tolerance boundary of the downstream side to form a safe range for pressure regulation. The calculation of the pressure regulation safety boundary is achieved by determining the upper and lower limits of the boundary. The upper limit is the upper limit of the driving pressure, and the lower limit is the preset target pressure setting value minus the disturbance pressure tolerance value. The target pressure setting value is the outlet pressure target value preset according to the operating requirements of the downstream steam-using equipment, which can be directly obtained from the pressure regulation control system of the mixer. The pressure regulation safety boundary is the range in which the mixer outlet pressure can be safely regulated under the current operating conditions, and all regulation actions must be carried out within this range. The physical significance of this step lies in integrating the dual boundary constraints of the high-pressure side and the downstream side, defining a safe and reasonable operating range for outlet pressure regulation. This ensures that the regulation action does not exceed the actual driving capacity of the high-pressure side, and that the pressure fluctuation after regulation does not exceed the tolerance range of the downstream load. For example, if the upper limit of the driving pressure is 0.35 MPa, the target pressure setting is 0.3 MPa, and the disturbance pressure tolerance is 0.0256 MPa, the calculated lower limit of the pressure regulation safety boundary is 0.2744 MPa, and the upper limit is 0.35 MPa. This indicates that the outlet pressure regulation needs to be controlled between 0.2744 MPa and 0.35 MPa. The technical effect of this step is that it achieves dynamic definition of the pressure regulation safety boundary. This boundary can be adjusted synchronously according to the real-time changes in the high-pressure side driving capacity and downstream load disturbances, ensuring that the pressure regulation range always matches the actual operating conditions of the equipment. This provides a safety guarantee for subsequent precise regulation and avoids equipment failure or regulation failure caused by regulation exceeding the boundary.

[0053] Obtain the preset target pressure setpoint, and obtain the outlet pressure dynamic balance coefficient based on the pressure regulation safety boundary and the target pressure setpoint. The outlet pressure dynamic balance coefficient is the normalized value of the ratio of the upper limit of the driving pressure to the disturbance pressure tolerance value under the constraint of the target pressure setpoint. This step is the core quantification of the dynamic balance state between the high-pressure side driving capability and the downstream load disturbance under the current operating conditions, and is a key link in connection state analysis and regulation command generation. The target pressure setpoint is retrieved in real time from the mixer's pressure regulation control system. The calculation of the outlet pressure dynamic balance coefficient follows the principle of first calculating the ratio and then normalizing. First, the driving pressure upper limit is calculated... The ratio of the limit value to the disturbance pressure tolerance value is then substituted into a normalization formula centered on the target pressure setpoint and within the range of the pressure regulation safety boundary. The normalization formula is: Dynamic balance coefficient = (ratio - minimum ratio) / (maximum ratio - minimum ratio), where the minimum ratio is the ratio of the lower limit of the pressure regulation safety boundary to the disturbance pressure tolerance value, and the maximum ratio is the ratio of the upper limit of the pressure regulation safety boundary to the disturbance pressure tolerance value. The outlet pressure dynamic balance coefficient obtained after normalization is a value between 0 and 1. This coefficient directly reflects the balance between the high-pressure side driving capacity and the downstream load disturbance under the current operating conditions, as well as the direction and magnitude of the adjustment required. The physical significance of this step lies in integrating the high-pressure side driving capability, downstream load disturbance, and target pressure setpoint into a quantitative coefficient that can directly guide the adjustment action. The magnitude and trend of the coefficient value correspond to the amplitude and direction of the outlet pressure adjustment. For example, the upper limit of the driving pressure is 0.35 MPa, the disturbance pressure tolerance is 0.0256 MPa, and the ratio of the two is 13.67. After normalization with the target pressure setpoint of 0.3 MPa as a constraint and the pressure adjustment safety boundary of 0.2744-0.35 MPa as a range, the outlet pressure dynamic balance coefficient is 0.65. This indicates that the high-pressure side driving capability and downstream load disturbance are in a moderate balance state at this time, and appropriate valve opening adjustment is required to approach the target pressure. The technical effect of this step is that it realizes the fusion and quantification of multi-dimensional operating status and target value, and transforms the boundary characteristics of the high-pressure side and downstream side and the target pressure setpoint into a single dynamic balance coefficient. This coefficient can accurately reflect the pressure balance status and regulation requirements under the current operating conditions, avoiding the complexity of multi-index analysis in traditional regulation methods, and providing a clear and quantitative basis for the generation of subsequent regulation commands.

[0054] The valve opening adjustment command is generated based on the outlet pressure dynamic balance coefficient, and the opening of the high-pressure steam inlet valve is controlled according to the valve opening adjustment command to make the actual pressure value at the mixer outlet approach the target pressure set value. This step is the execution link of the entire pressure stabilization and regulation method, which transforms the previous quantitative analysis results into specific valve control actions to achieve precise dynamic regulation of the outlet pressure. The generation of the valve opening adjustment command is based on the mapping relationship between the outlet pressure dynamic balance coefficient and the valve opening. This mapping relationship is obtained through industrial tests and equipment operation data calibration and is pre-stored in the pressure regulation and control system of the mixer. The mapping relationship follows the linear regulation principle, that is, the outlet pressure dynamic balance coefficient is positively correlated with the valve opening. The higher the coefficient value, the greater the corresponding valve opening adjustment range. The high-pressure steam inlet valve is an electric regulating valve, which can receive electrical signal commands from the regulation and control system and execute corresponding opening actions. The regulation and control system sends an electrical signal to the high-pressure steam inlet valve according to the generated valve opening adjustment command to control the valve opening to increase or decrease, thereby adjusting the steam inlet flow of high-pressure steam, changing the driving capability of the high-pressure side, and finally realizing the convergence of the actual pressure value at the mixer outlet to the target pressure set value. The physical significance of this step lies in dynamically adjusting the high-pressure steam intake through precise valve opening control. This achieves a dynamic rebalancing of the high-pressure side driving capability and downstream load disturbances, ensuring the outlet pressure consistently approaches the target setpoint. For example, if the outlet pressure dynamic balance coefficient is 0.65, the valve opening adjustment command generated based on the mapping relationship would be to adjust the valve opening from the current 40% to 50%. Upon receiving this command, the high-pressure steam inlet valve increases its opening by 10%, correspondingly increasing the steam intake. This enhances the high-pressure side driving capability, and the actual pressure at the mixer outlet gradually approaches the target setpoint of 0.3MPa from 0.28MPa. The technical effect of this step is the precise conversion from a quantitative coefficient to a control action. Valve opening adjustment based on the dynamic balance coefficient can adjust the adjustment range according to the real-time operating status of the equipment. Compared to traditional fixed-step adjustment, this method offers higher adjustment accuracy and more timely response, quickly achieving dynamic pressure stabilization of the outlet pressure. This ensures the outlet pressure remains stable near the target setpoint even under dynamic changes on the high-pressure and downstream sides.

[0055] like Figure 2 As shown, this application also provides a steam jet mixer outlet pressure stabilization and regulation system, comprising: The first acquisition module is used to acquire the operating parameters of the steam jet mixer, wherein the operating parameters include high-pressure steam inlet pressure data, low-pressure steam inlet pressure data and actual outlet pressure values; The second acquisition module is used to acquire the reference driving pressure and high-pressure steam fluctuation data based on the high-pressure steam inlet pressure data, and to acquire the driving pressure dynamic response coefficient based on the reference driving pressure and high-pressure steam fluctuation data. The third acquisition module is used to acquire the ejector end pressure value and ejector flow rate data based on the low-pressure steam inlet pressure data, and to acquire the ejector structure sensitivity coefficient based on the ejector end pressure value and ejector flow rate data. The fourth acquisition module is used to acquire the high-pressure side driving capability coefficient based on the driving pressure dynamic response coefficient and the ejector structure sensitivity coefficient. The fifth acquisition module is used to acquire a real-time outlet pressure sequence and pressure fluctuation spectrum based on the actual outlet pressure value, and to acquire a downstream load disturbance coefficient based on the real-time outlet pressure sequence and the pressure fluctuation spectrum. The adjustment module is used to obtain the outlet pressure dynamic balance coefficient based on the high-pressure side drive capability coefficient and the downstream load disturbance coefficient, and to adjust the outlet pressure of the steam jet mixer based on the outlet pressure dynamic balance coefficient.

[0056] In one embodiment, the second acquisition module includes: The first acquisition unit is used to acquire historical pressure time series data of the high-pressure steam inlet within a preset historical time period, and to acquire the pressure reference stable value of the high-pressure steam based on the historical pressure time series data, and to use the pressure reference stable value as the reference driving pressure. The second acquisition unit is used to acquire the real-time pressure value at the current moment based on the high-pressure steam inlet pressure data, and to acquire the pressure transient deviation value based on the real-time pressure value and the reference driving pressure. The sampling unit is used to perform sliding sampling on the high-pressure steam inlet pressure data within a unit time window to obtain a pressure instantaneous fluctuation sequence, and to calculate the root mean square value of the fluctuation based on the pressure instantaneous fluctuation sequence, and to use the root mean square value of the fluctuation as the high-pressure steam fluctuation data. The third acquisition unit is used to acquire the pressure response amplitude factor based on the pressure transient deviation value and the root mean square value of the fluctuation, and to perform a fast Fourier transform on the pressure instantaneous fluctuation sequence to obtain the fluctuation spectrum energy distribution, and to acquire the proportion of high-frequency fluctuation energy based on the fluctuation spectrum energy distribution. The fourth acquisition unit is used to acquire the driving pressure dynamic response coefficient based on the pressure response amplitude factor and the high-frequency fluctuation energy ratio, wherein the driving pressure dynamic response coefficient characterizes the pressure recovery capability of the high-pressure steam source under unit disturbance.

[0057] This application also provides a computer device, including a memory and a processor, wherein the memory stores a computer program, and the processor executes the computer program to implement the steps of the above-described method.

[0058] This application also provides a computer-readable storage medium having a computer program stored thereon, which, when executed by a processor, implements the steps of the above-described method.

[0059] Those skilled in the art will understand that all or part of the processes in the methods of the above embodiments can be implemented by a computer program instructing related hardware. The computer program can be stored in a non-volatile computer-readable storage medium, and when executed, it can include the processes of the embodiments of the methods described above. Any references to memory, storage, databases, or other media used in this application and in the embodiments can include non-volatile and / or volatile memory. Non-volatile memory can include read-only memory (ROM), programmable ROM (PROM), electrically programmable ROM (EPROM), electrically erasable programmable ROM (EEPROM), or flash memory. Volatile memory can include random access memory (RAM) or external cache memory. By way of illustration and not limitation, RAM is available in various forms, such as static RAM (SRAM), dynamic RAM (DRAM), synchronous DRAM (SDRAM), dual data rate SDRAM (SSRSDRAM), enhanced SDRAM (ESDRAM), synchronous link DRAM (SLDRAM), Rambus direct RAM (RDRAM), direct memory bus dynamic RAM (DRDRAM), and memory bus dynamic RAM (RDRAM), etc.

[0060] It should be noted that, in this document, the terms "comprising," "including," or any other variations thereof are intended to cover non-exclusive inclusion, such that a process, apparatus, article, or method that comprises a list of elements includes not only those elements but also other elements not expressly listed, or elements inherent to such a process, apparatus, article, or method. Unless otherwise specified, an element defined by the phrase "comprising one..." does not exclude the presence of other identical elements in the process, apparatus, article, or method that includes that element.

[0061] The above description is merely a preferred embodiment of the present invention and does not limit the patent scope of the present invention. Any equivalent structural or procedural transformations made based on the content of the present invention's specification and drawings, or direct or indirect applications in other related technical fields, are similarly included within the patent protection scope of the present invention.

Claims

1. A method for regulating the outlet pressure of a steam jet mixer, characterized in that, include: Obtain the operating parameters of the steam jet mixer, wherein the operating parameters include high-pressure steam inlet pressure data, low-pressure steam inlet pressure data, and actual outlet pressure values; Based on the high-pressure steam inlet pressure data, a reference driving pressure and high-pressure steam fluctuation data are obtained, and based on the reference driving pressure and high-pressure steam fluctuation data, a dynamic response coefficient of the driving pressure is obtained, including: Acquire historical pressure time series data of the high-pressure steam inlet within a preset historical time period, and obtain the pressure reference stable value of the high-pressure steam based on the historical pressure time series data, and use the pressure reference stable value as the reference driving pressure. The real-time pressure value at the current moment is obtained based on the high-pressure steam inlet pressure data, and the pressure transient deviation value is obtained based on the real-time pressure value and the reference driving pressure. The pressure data at the high-pressure steam inlet is sampled within a unit time window to obtain a pressure instantaneous fluctuation sequence. The root mean square value of the fluctuation is calculated based on the pressure instantaneous fluctuation sequence, and the root mean square value of the fluctuation is used as the high-pressure steam fluctuation data. The pressure response amplitude factor is obtained based on the pressure transient deviation value and the root mean square value of the fluctuation, and a fast Fourier transform is performed on the pressure instantaneous fluctuation sequence to obtain the fluctuation spectrum energy distribution. The proportion of high-frequency fluctuation energy is obtained based on the fluctuation spectrum energy distribution. The dynamic response coefficient of the driving pressure is obtained based on the pressure response amplitude factor and the proportion of high-frequency fluctuation energy. Based on the low-pressure steam inlet pressure data, the ejector end pressure value and ejector flow rate data are obtained, and the ejector structure sensitivity coefficient is obtained based on the ejector end pressure value and ejector flow rate data, including: Obtain the pressure sequence of the low-pressure steam inlet within a continuous time window, calculate the pressure change rate sequence based on the pressure sequence, and use the current value of the pressure sequence as the ejector end pressure value. Obtain the geometric parameters of the mixer ejector cavity, and calculate the theoretical maximum ejector flow rate based on the geometric parameters and the ejector end pressure value, and use the theoretical maximum ejector flow rate as the reference ejector flow rate; Obtain the real-time flow rate detection value of the low-pressure steam inlet, and obtain the flow rate deviation ratio based on the real-time flow rate detection value and the reference ejector flow rate; Kalman filtering is applied to the pressure change rate sequence to obtain a smoothed pressure change rate, and the flow resistance change gradient of the ejector cavity is obtained based on the smoothed pressure change rate and the flow deviation ratio. The sensitivity coefficient of the ejector structure is obtained based on the flow resistance change gradient and the geometric parameters of the ejector cavity; The high-pressure side driving capability coefficient is obtained based on the driving pressure dynamic response coefficient and the ejector structure sensitivity coefficient, including: Obtain the nozzle throat area parameters and nozzle outlet area parameters of the high-pressure steam inlet, and calculate the nozzle expansion ratio based on the nozzle throat area parameters and the nozzle outlet area parameters; The jet flow correction factor for high-pressure steam is obtained based on the driving pressure dynamic response coefficient and the expansion ratio. The momentum exchange efficiency coefficient of the mixing chamber is obtained based on the sensitivity coefficient of the ejector structure and the ejector momentum correction factor. The high-pressure side driving capability coefficient is obtained based on the momentum exchange efficiency coefficient and the real-time pressure value of the high-pressure steam inlet. Based on the actual value of the outlet pressure, a real-time outlet pressure sequence and pressure fluctuation spectrum are obtained, and the downstream load disturbance coefficient is obtained based on the real-time outlet pressure sequence and the pressure fluctuation spectrum, including: The actual value of the outlet pressure is continuously collected at a preset sampling frequency to obtain the real-time outlet pressure sequence. Empirical mode decomposition is performed on the real-time outlet pressure sequence to obtain multiple intrinsic mode function components, and the intrinsic mode function components with frequencies higher than the preset cutoff frequency are taken as high-frequency pressure fluctuation components. The high-frequency pressure fluctuation components are subjected to Hilbert transform to obtain the instantaneous pressure fluctuation amplitude sequence and the instantaneous pressure fluctuation frequency sequence; The cumulative pressure fluctuation energy per unit time is calculated based on the instantaneous pressure fluctuation amplitude sequence, and the dominant frequency offset of the pressure fluctuation is calculated based on the instantaneous pressure fluctuation frequency sequence. The downstream load disturbance coefficient is obtained based on the accumulated energy value of the pressure fluctuation and the main frequency offset of the pressure fluctuation; The outlet pressure dynamic balance coefficient is obtained based on the high-pressure side drive capability coefficient and the downstream load disturbance coefficient, and the outlet pressure of the steam jet mixer is adjusted according to the outlet pressure dynamic balance coefficient, including: The theoretical maximum output pressure of the high-pressure side under the current operating conditions is obtained based on the high-pressure side drive capability coefficient, and the theoretical maximum output pressure is used as the upper limit of the drive pressure. The downstream pressure bearing margin under the current operating conditions is obtained based on the downstream load disturbance coefficient, and the pressure bearing margin is used as the disturbance pressure tolerance value. The pressure regulation safety boundary is obtained based on the upper limit of the driving pressure and the disturbance pressure tolerance value; Obtain a preset target pressure setting value, and obtain an outlet pressure dynamic balance coefficient based on the pressure adjustment safety boundary and the target pressure setting value, wherein the outlet pressure dynamic balance coefficient is a normalized value of the ratio of the upper limit of the driving pressure to the disturbance pressure tolerance value under the constraint of the target pressure setting value. A valve opening adjustment command is generated based on the outlet pressure dynamic balance coefficient, and the opening of the high-pressure steam inlet valve is controlled according to the valve opening adjustment command so that the actual pressure value at the mixer outlet approaches the target pressure setting value.

2. A steam jet mixer outlet pressure stabilization and regulation system, used to execute the steam jet mixer outlet pressure stabilization and regulation method as described in claim 1, characterized in that, include: The first acquisition module is used to acquire the operating parameters of the steam jet mixer, wherein the operating parameters include high-pressure steam inlet pressure data, low-pressure steam inlet pressure data and actual outlet pressure values; The second acquisition module is used to acquire the reference driving pressure and high-pressure steam fluctuation data based on the high-pressure steam inlet pressure data, and to acquire the driving pressure dynamic response coefficient based on the reference driving pressure and high-pressure steam fluctuation data. The third acquisition module is used to acquire the ejector end pressure value and ejector flow rate data based on the low-pressure steam inlet pressure data, and to acquire the ejector structure sensitivity coefficient based on the ejector end pressure value and ejector flow rate data. The fourth acquisition module is used to acquire the high-pressure side driving capability coefficient based on the driving pressure dynamic response coefficient and the ejector structure sensitivity coefficient. The fifth acquisition module is used to acquire a real-time outlet pressure sequence and pressure fluctuation spectrum based on the actual outlet pressure value, and to acquire the downstream load disturbance coefficient based on the real-time outlet pressure sequence and the pressure fluctuation spectrum. The adjustment module is used to obtain the outlet pressure dynamic balance coefficient based on the high-pressure side drive capability coefficient and the downstream load disturbance coefficient, and to adjust the outlet pressure of the steam jet mixer based on the outlet pressure dynamic balance coefficient.

3. The steam jet mixer outlet pressure stabilization and regulation system according to claim 2, characterized in that, The second acquisition module includes: The first acquisition unit is used to acquire historical pressure time series data of the high-pressure steam inlet within a preset historical time period, and to acquire the pressure reference stable value of the high-pressure steam based on the historical pressure time series data, and to use the pressure reference stable value as the reference driving pressure. The second acquisition unit is used to acquire the real-time pressure value at the current moment based on the high-pressure steam inlet pressure data, and to acquire the pressure transient deviation value based on the real-time pressure value and the reference driving pressure. The sampling unit is used to perform sliding sampling of the high-pressure steam inlet pressure data within a unit time window to obtain a pressure instantaneous fluctuation sequence, and to calculate the root mean square value of the fluctuation based on the pressure instantaneous fluctuation sequence, and to use the root mean square value of the fluctuation as the high-pressure steam fluctuation data. The third acquisition unit is used to acquire the pressure response amplitude factor based on the pressure transient deviation value and the root mean square value of the fluctuation, and to perform a fast Fourier transform on the pressure instantaneous fluctuation sequence to obtain the fluctuation spectrum energy distribution, and to acquire the proportion of high-frequency fluctuation energy based on the fluctuation spectrum energy distribution. The fourth acquisition unit is used to acquire the dynamic response coefficient of the driving pressure based on the pressure response amplitude factor and the proportion of high-frequency fluctuation energy.

4. A computer device comprising a memory and a processor, wherein the memory stores a computer program, characterized in that, When the processor executes the computer program, it implements the steps of the method of claim 1.

5. A computer-readable storage medium having a computer program stored thereon, characterized in that, When the computer program is executed by a processor, it implements the steps of the method of claim 1.

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