Driving power supply fault switching method and system

Abstract

The invention discloses a driving power supply fault switching method and system, particularly relates to the technical field of power system relay protection, and is used for solving the problem that an existing relay power supply switching system causes misoperation due to common-mode interference caused by ground fault transient potential gradient. An earth screen potential gradient is collected in real time, a control cable orthogonal electric field component is measured synchronously, an electric field fiber bundle structure is reconstructed based on topology invariant distribution of a cable surface topology sequence substance, and a common-mode interference coupling coefficient is generated according to a space vector relation between an earth screen gradient direction and a reconstructed electric field; the coupling coefficient is converted into electrostrictive strain through the inverse piezoelectric effect, then a dynamic compensation voltage instruction is generated, finally, the compensation instruction is superposed to a power supply control loop to drive a standby power supply to be switched, the coupling influence of earth screen transient interference on a relay is eliminated from the physical mechanism level, the problem of misoperation is fundamentally solved, and the reliability of the relay is improved. And the reliability of power supply switching of the ultrahigh-voltage power transmission and transformation system is

Description

Technical Field

[0001] The present invention relates to the technical field of power system relay protection, and in particular to a driving power supply fault switching method and system. Background Art

[0002] In high-voltage power transmission and transformation systems, particularly AC transmission networks above 750 kV, redundant switching devices for drive power supplies are critical infrastructure for ensuring uninterrupted operation of core equipment. Existing technologies generally employ a control architecture based on relay logic, triggering the switching of backup power sources by real-time monitoring of the primary power supply status. Such systems are typically deployed around the substation grounding grid, with control cables sharing the same grounding system as primary equipment. When the power grid is struck by lightning or suffers a short-circuit fault, the fault current is discharged through the grounding grid, generating a transient potential distribution.

[0003] The current power switching system faces a flaw: the transient potential gradient changes caused by ground faults will induce high-intensity common-mode interference voltage in the switching control loop through the parasitic coupling path between the control cable and the grounding grid. This interference, generated by the coupling of the electromagnetic environment and the inherent characteristics of the equipment layout, causes unpredictable malfunctions or refusal to operate of the relay actuator, seriously undermining the reliability of the power switching timing. Especially in large-scale power grid security scenarios, such hidden failures may cause cascading system failures. Summary of the Invention

[0004] The present invention aims to solve the technical problems existing in the prior art and provides a driving power supply fault switching method and system.

[0005] The technical solution of the present invention to solve the above technical problems is as follows:

[0006] The present invention provides the following technical solutions:

[0007] The driving power supply failure switching method includes:

[0008] S1, real-time acquisition of ground grid potential gradient amplitude and distribution direction when the ground grid fails;

[0009] S2. When the grid potential gradient amplitude exceeds a preset safety threshold, synchronously measure the orthogonal electric field intensity components on the control cable path;

[0010] S3, detecting the topological invariant distribution of the topologically ordered material on the surface of the control cable, and reconstructing the fiber bundle structure of the orthogonal electric field intensity components based on the gauge invariance mapping relationship between the topological invariant distribution and the orthogonal electric field intensity components;

[0011] S4. Generate a common-mode interference coupling coefficient based on the spatial vector relationship between the ground grid potential gradient distribution direction and the reconstructed orthogonal electric field strength components;

[0012] S5. Determine the electrostrictive tensor of the relay insulation medium according to the common-mode interference coupling coefficient, and generate a dynamic compensation voltage command through the intrinsic relationship between strain and electric field in the inverse piezoelectric effect;

[0013] S6. Superimpose the dynamic compensation voltage instruction on the power supply switching control circuit to drive the standby power supply switching actuator.

[0014] Furthermore, the ground grid potential gradient amplitude and distribution direction are collected in real time when the ground grid fails, including:

[0015] Deploy an array of magnetic induction probes at the intersection of ground grid conductors;

[0016] The direction of the transient magnetic field generated by the fault current is synchronously measured by an array of magnetic induction probes;

[0017] According to the spatial correlation between the transient magnetic field direction and the geometric structure of the grounding grid conductor, the grounding grid potential gradient amplitude and grounding grid potential gradient distribution direction are generated.

[0018] Furthermore, the distribution density of the magnetic induction probe array is positively correlated with the conductor crossing complexity.

[0019] Furthermore, when the grid potential gradient amplitude exceeds a preset safety threshold, the orthogonal electric field strength components on the control cable path are synchronously measured, including:

[0020] Multiple groups of three-dimensional electric field probes are set on the control cable path, and each group of three-dimensional electric field probes includes three mutually perpendicular electric field sensors;

[0021] When the grid potential gradient amplitude exceeds the preset safety threshold, all three-dimensional electric field probes are activated simultaneously;

[0022] The three mutually perpendicular electric field sensors of each set of three-dimensional electric field probes are used to measure the electric field strength in three orthogonal directions at corresponding positions on the control cable path;

[0023] The electric field intensities in three orthogonal directions at each measurement position are combined to form orthogonal electric field intensity components.

[0024] Furthermore, the topological invariant distribution of the topologically ordered material on the surface of the control cable is detected, and the fiber bundle structure of the orthogonal electric field intensity components is reconstructed based on the gauge invariance mapping relationship between the topological invariant distribution and the orthogonal electric field intensity components, including:

[0025] Angle-resolved photoelectron spectroscopy is used to scan the surface of the control cable shield to obtain the electronic band structure of topologically ordered materials.

[0026] The spatial distribution parameters of Chern number and Berry curvature are extracted from the electronic band structure as topological invariant distribution;

[0027] Establish the gauge invariance mapping relationship between the topological invariant distribution and the orthogonal electric field intensity components;

[0028] The spatial vector directions of the orthogonal electric field intensity components are corrected according to the gauge invariance mapping relationship to form a fiber bundle structure of the orthogonal electric field intensity components.

[0029] Furthermore, based on the spatial vector relationship between the ground grid potential gradient distribution direction and the reconstructed orthogonal electric field strength components, a common mode interference coupling coefficient is generated, including:

[0030] Obtain the unit direction vector corresponding to the ground grid potential gradient distribution direction;

[0031] Extract the electric field vector of the reconstructed orthogonal electric field intensity component projected on the grounding grid plane;

[0032] Calculate the angle between the unit direction vector and the electric field vector;

[0033] The common-mode interference coupling coefficient is generated according to the product relationship between the direction angle and the electric field vector modulus.

[0034] Furthermore, the electrostrictive tensor of the relay insulation medium is determined according to the common-mode interference coupling coefficient, and a dynamic compensation voltage instruction is generated through the intrinsic relationship between strain and electric field in the inverse piezoelectric effect, including:

[0035] According to the corresponding relationship between the common mode interference coupling coefficient and the parameters of the relay insulation medium material, the electrostrictive tensor component is determined;

[0036] Calculate the strain distribution of relay insulation under common mode interference through electrostrictive tensor components;

[0037] According to the intrinsic relationship between strain and electric field in the inverse piezoelectric effect, the strain distribution is converted into the compensation electric field intensity distribution;

[0038] A dynamic compensation voltage command is generated based on the integration of the compensation electric field intensity distribution along the relay contact spacing direction.

[0039] Furthermore, according to the intrinsic relationship between strain and electric field in the inverse piezoelectric effect, the strain distribution is converted into the compensation electric field intensity distribution, which includes:

[0040] Through the linear constitutive relationship between strain tensor and electric field intensity in the inverse piezoelectric effect, the strain state of each point inside the relay insulation medium is directly converted into the compensation electric field intensity value at the corresponding spatial position;

[0041] The strain tensor component and the electric field intensity component establish a conversion relationship through the electrostrictive coefficient matrix to form a spatial mapping of the compensation electric field intensity distribution.

[0042] Furthermore, the dynamic compensation voltage command is superimposed on the power supply switching control loop to drive the backup power supply switching actuator, including:

[0043] Obtaining the voltage amplitude and timing waveform of the dynamic compensation voltage instruction;

[0044] coupling the dynamic compensation voltage command to the control signal transmission line of the power switching control loop through an isolation amplifier;

[0045] In the relay coil excitation time window, the coupled dynamic compensation voltage command is injected into the power switching control loop;

[0046] According to the injected power switching control circuit driving signal, the action coil of the standby power switching actuator is triggered.

[0047] In another aspect, the present invention provides a drive power supply fault switching system, comprising:

[0048] Gradient monitoring module, used to collect the ground grid potential gradient amplitude and distribution direction in real time when the ground grid fails;

[0049] The electric field measurement module is used to synchronously measure the orthogonal electric field intensity components on the control cable path when the grid potential gradient amplitude exceeds a preset safety threshold;

[0050] A topology reconstruction module is used to detect the topological invariant distribution of the topologically ordered material on the surface of the control cable and reconstruct the fiber bundle structure of the orthogonal electric field intensity components based on the gauge invariance mapping relationship between the topological invariant distribution and the orthogonal electric field intensity components;

[0051] A coupling generation module is used to generate a common-mode interference coupling coefficient based on the spatial vector relationship between the ground grid potential gradient distribution direction and the reconstructed orthogonal electric field strength components;

[0052] A voltage generation module is used to determine the electrostrictive tensor of the relay insulation medium based on the common-mode interference coupling coefficient, and to generate a dynamic compensation voltage command through the intrinsic relationship between strain and electric field in the inverse piezoelectric effect;

[0053] The switching drive module is used to superimpose the dynamic compensation voltage instruction on the power switching control loop to drive the backup power switching actuator.

[0054] The beneficial effects of the present invention are:

[0055] 1. By establishing a physical connection between the transient interference of the ground grid and the electric field of the cable, the problem of relay malfunction caused by ground faults is solved. First, based on the gauge invariance mapping of topologically ordered matter, the electric field fiber bundle structure is reconstructed, and the quantum state characteristics of the cable surface are correlated with the macroscopic electromagnetic response. The real common-mode interference component induced by the ground grid potential gradient on the cable path is accurately separated, eliminating the measurement distortion caused by the ambiguity of the electromagnetic coupling path in traditional technologies. Secondly, the intrinsic relationship between strain and electric field in the inverse piezoelectric effect is utilized. The relay insulation medium is used as an active compensation element, and the reverse offset electric field is dynamically generated through the electrostrictive tensor. The contamination of the actuator drive signal by common-mode interference is eliminated at the physical level, eliminating the risk of false triggering at the mechanism level.

[0056] 2. Significantly improve the operational reliability of the power switching system in strong electromagnetic interference environments. Through closed-loop control of space vector projection and dynamic compensation voltage, anti-interference compensation signals are injected into the relay excitation window in real time to ensure that the actuator only operates in the event of a real power failure. Electromagnetic environmental disturbances are incorporated into the control variables, giving the switching system the ability to adapt to the transient potential of the ground grid. This is particularly suitable for scenarios with multiple ground loops in ultra-high voltage substations, effectively avoiding cascading failures caused by hidden coupling interference and providing precise power supply guarantee for core equipment of the smart grid. BRIEF DESCRIPTION OF THE DRAWINGS

[0057] Figure 1 This is a flow chart of a method for switching a driving power supply failure according to the present invention;

[0058] Figure 2 It is a structural diagram of the driving power supply failure switching system of the present invention. DETAILED DESCRIPTION

[0059] The following will clearly and completely describe the technical solutions in the embodiments of the present invention in conjunction with the accompanying drawings. Obviously, the described embodiments are only part of the embodiments of the present invention, not all of the embodiments. Based on the embodiments of the present invention, all other embodiments obtained by ordinary technicians in this field without making creative efforts are within the scope of protection of the present invention.

[0060] Example 1: Figure 1 A drive power supply fault switching method of the present invention is provided, comprising:

[0061] S1, real-time acquisition of ground grid potential gradient amplitude and distribution direction when the ground grid fails;

[0062] S2. When the grid potential gradient amplitude exceeds a preset safety threshold, synchronously measure the orthogonal electric field intensity components on the control cable path;

[0063] S3, detecting the topological invariant distribution of the topologically ordered material on the surface of the control cable, and reconstructing the fiber bundle structure of the orthogonal electric field intensity components based on the gauge invariance mapping relationship between the topological invariant distribution and the orthogonal electric field intensity components;

[0064] S4. Generate a common-mode interference coupling coefficient based on the spatial vector relationship between the ground grid potential gradient distribution direction and the reconstructed orthogonal electric field strength components;

[0065] S5. Determine the electrostrictive tensor of the relay insulation medium according to the common-mode interference coupling coefficient, and generate a dynamic compensation voltage command through the intrinsic relationship between strain and electric field in the inverse piezoelectric effect;

[0066] S6. Superimpose the dynamic compensation voltage instruction on the power supply switching control circuit to drive the standby power supply switching actuator.

[0067] S1. Real-time acquisition of the ground grid potential gradient amplitude and distribution direction when the ground grid fails. The specific implementation is as follows:

[0068] Magnetic induction probe arrays are deployed at the intersection of grounding grid conductors. The density of the magnetic induction probe array is positively correlated with the conductor intersection complexity. Conductor intersection complexity is determined based on the number of conductors at the intersection and the sharpness of the angles between them. Specifically, the greater the number of conductors and the smaller the angles between them, the higher the conductor intersection complexity. Conductor intersection complexity is quantified by multiplying the number of conductors by the inverse of the cosine of the conductor angle, where the conductor angle refers to the acute angle formed at the conductor intersection. The magnetic induction probe array uses a Rogowski coil structure. Each magnetic induction probe has a sensitivity of, for example, 0.1 volts per Tesla and a frequency response range of, for example, 10 Hz to 1 MHz. The spacing between magnetic induction probes is dynamically adjusted based on the conductor intersection complexity. For example, when the conductor intersection complexity exceeds a preset complexity threshold, the magnetic induction probe spacing is reduced to 50 cm to 100 cm. When the conductor intersection complexity is below the preset complexity threshold, the magnetic induction probe spacing is increased to 150 cm to 200 cm. The preset complexity threshold is set by statistically analyzing the mean value of conductor crossing characteristics in areas with a historical failure rate higher than 90% through grounding grid design drawings.

[0069] The transient magnetic field direction generated by the fault current is synchronously measured by an array of magnetic induction probes. The time accuracy of the synchronous measurement is controlled within 0.1 microseconds, and the global positioning system second pulse signal is used as the time synchronization reference. The measurement process of the transient magnetic field direction includes: each magnetic induction probe captures the waveform data of the magnetic field intensity changing with time, and the waveform data sampling rate is, for example, 1 MHz; the sudden change section with a magnetic field intensity change rate exceeding 10 amperes per microsecond is extracted from the waveform data as the fault current characteristic section; the spatial orientation of the magnetic field vector is calculated within the fault current characteristic section, and the spatial orientation is expressed as the azimuth and pitch angle in the geodetic coordinate system. The azimuth is calculated based on the inverse tangent function value of the horizontal component of the magnetic field, and the pitch angle is calculated based on the inverse tangent function value of the modulus of the vertical component and the horizontal component of the magnetic field.

[0070] Based on the spatial correlation between the transient magnetic field direction and the geometric structure of the grounding grid conductor, the grounding grid potential gradient amplitude and grounding grid potential gradient distribution direction are generated. The process of establishing the spatial correlation includes: obtaining the three-dimensional coordinate data of the grounding grid conductor, the three-dimensional coordinate data comes from the digital model of the grounding grid as-built drawings; inputting the transient magnetic field direction data and the three-dimensional coordinate data of the grounding grid conductor into the electromagnetic field integral equation, the electromagnetic field integral equation is in the form of a closed path magnetic field loop integral equal to the algebraic sum of the conductor currents enclosed by the path. The specific process of calculating the grounding grid potential gradient amplitude is as follows: select two adjacent conductor nodes of the grounding grid as the endpoints of the calculation path; perform a line integration of the tangential component of the magnetic field along the calculation path, and divide the integral result by the vacuum permeability 4π×10 -7 The potential difference is calculated in henries per meter. Dividing the potential difference by the calculated path length yields the ground grid potential gradient amplitude, expressed in volts per meter. The direction of the ground grid potential gradient distribution is determined by establishing a two-dimensional rectangular coordinate system on the ground grid plane. The unit vector of the calculated path direction vector is used as the ground grid potential gradient distribution direction. The direction is expressed as the angle with the positive x-axis of the coordinate system, ranging from 0 to 360 degrees.

[0071] Identifying ground grid conductor intersections is accomplished through the following steps: importing the three-dimensional coordinate data of the ground grid conductors; calculating the spatial distance between all conductor segments; and determining a conductor intersection when the spatial distance between two conductors is less than three times the conductor diameter and the conductors are non-parallel. The boundary of the conductor intersection is defined as a circular area centered at the intersection with a radius of 2 to 5 meters, with the specific radius being positively correlated with the conductor's cross-sectional area. The installation accuracy requirements for the magnetic induction probe array are: horizontal positioning error less than 10 cm, and vertical positioning error less than 5 cm. The positioning reference point is the permanent coordinate marker of the ground grid test stake.

[0072] The fault current characteristic segment identification criteria for transient magnetic field direction measurement are: the current rate of change threshold is set between 5 kA / ms and 10 kA / ms. The specific threshold is determined based on the substation's short-circuit capacity: for example, 10 kA / ms for a 220 kV substation, 7 kA / ms for a 110 kV substation, and 5 kA / ms for a 35 kV substation. The spatial orientation calculation of the magnetic field vector requires temperature compensation with a coefficient of -0.05% to -0.1% per degree Celsius. This compensation data is derived from real-time monitoring values ​​from the magnetic induction probe's built-in temperature sensor.

[0073] The path length selection principle for calculating the ground grid potential gradient amplitude is as follows: when the conductor spacing is less than 1 meter, the actual spacing is used directly; when the conductor spacing is greater than 1 meter, a segmented integration method is used, with segment lengths no longer than 1 meter. The angular resolution of the potential gradient distribution direction is set to 0.1 degrees, and the angular reference is regularly calibrated using total station measurements, with a calibration period no longer than 3 months. All generated ground grid potential gradient amplitude and distribution direction data are stored in real-time in non-volatile memory as a timestamp-tagged floating-point array with a timestamp accuracy of 1 millisecond.

[0074] The spatial correlation of the grounding grid's conductor geometry is verified by injecting a test current of 1 kHz to 10 kHz, with an amplitude of 1 ampere to 10 amperes, into the grounding grid. An array of magnetic induction probes is used to measure the spatial magnetic field distribution. The measured magnetic field direction is compared with the theoretically calculated direction. A calibration mode is triggered when the deviation exceeds 5 degrees. This calibration mode also involves recalibrating the magnetic induction probe's installation angle offset, which is measured using a laser theodolite with a measurement accuracy of 0.01 degrees.

[0075] The dynamic adjustment mechanism for conductor crossing complexity is as follows: when the fault current amplitude in a certain area exceeds 10 kiloamperes three times in a row, the density of magnetic induction probes in that area is automatically increased by 1.5 to 2 times the original density. The deployment locations of the new magnetic induction probes are determined through finite element simulation. The simulation model considers the conductivity of the conductor material to be 5.8×10 7 Siemens copper conductor parameters per meter with a relative magnetic permeability of 1.0 require a mesh size no larger than one-tenth of the conductor diameter. When measuring the transient magnetic field direction generated by the fault current, anti-interference measures include: using twisted-pair shielded cable for signal transmission with multiple grounding points on the shield; installing a 50 Hz to 60 Hz band-stop filter in the signal conditioning circuit with a stopband attenuation greater than 40 decibels; and installing a gas discharge tube at the front end of the data acquisition card, with the discharge trigger voltage set to 600 volts.

[0076] The data verification process for generating the ground grid potential gradient amplitude is as follows: simultaneously use a voltage probe to directly measure the potential difference between the conductor nodes, and the voltage probe input impedance is greater than 10 megohms; when the deviation between the magnetic induction measurement result and the direct measurement result exceeds 15%, start the fault diagnosis program. The fault diagnosis program includes checking the on-resistance of the magnetic induction probe connection line, the signal amplifier gain setting, and the ground grid corrosion condition detection. The ground grid corrosion detection adopts the DC potential drop method, and the test current is 10 amperes DC current. The final output ground grid potential gradient distribution direction data format is a composite structure containing the direction angle value and the confidence level. The confidence level is determined according to the product value of the measurement path length and the fault current amplitude: for example, the product value is greater than 10 5 The confidence level is level 1 when the ampere meter is 10 4 Ampere-meter to 10 5 Ampere-meter is level 2, less than 10 4 The ampere-meter is level three.

[0077] S2. When the grid potential gradient amplitude exceeds the preset safety threshold, synchronously measure the orthogonal electric field strength components on the control cable path. The specific implementation is as follows:

[0078] Multiple sets of three-dimensional electric field probes are installed along the control cable path. Each set of three-dimensional electric field probes contains three mutually perpendicular electric field sensors. The control cable path is defined as a parallel spatial trajectory 5 to 10 cm from the surface of the cable outer sheath. The length of the path segment is determined by the cable bending radius: for example, a set of probes is installed every 20 meters on a straight section, and a set of probes is installed every 5 meters on a curved section. The three-dimensional electric field probes are installed by fixing them to the cable bracket using a non-magnetic clamp. The central axis of the probe is parallel to the cable axis, and the installation position error is controlled within ±2 cm. The axial angle calibration accuracy of the three mutually perpendicular electric field sensors is 90 ± 0.1 degrees. The calibration method uses laser interferometer measurement, and the calibration reference source is a 1 kilovolt per meter standard electric field generator.

[0079] When the grid potential gradient amplitude exceeds the preset safety threshold, all three-dimensional electric field probes are activated simultaneously. The preset safety threshold is set based on the insulation level of the control cable and historical fault statistics: for example, for a 35 kV cable system, the preset safety threshold is set at 800 volts per meter; for a 110 kV cable system, it is set at 1500 volts per meter. The activation signal is transmitted using a fiber-optic synchronous network with a synchronization time deviation of less than 100 nanoseconds. The activation logic includes: real-time reception of the grid potential gradient amplitude data output by step S1; when the amplitudes of three consecutive sampling points exceed the preset safety threshold, an activation command is sent to the probe power controller; the power controller switches the probe power supply voltage from the standby state of 5 volts to the working state of 24 volts, and the switching response time is less than 10 microseconds.

[0080] Each set of three-dimensional electric field probes uses three mutually perpendicular electric field sensors to measure the electric field strength in three orthogonal directions at corresponding locations along the control cable path. The measurement process is implemented as follows: the three orthogonal directions are defined as the X-axis (east-west), Y-axis (north-south), and Z-axis (vertical) of the geodetic coordinate system. Each electric field sensor has a measurement range of 0 to 10 kilovolts per meter, a resolution of 0.1 volts per meter, and a bandwidth from DC to 1 MHz. Data acquisition utilizes synchronous sampling, with the sampling rate dynamically adjusted based on the interference frequency: for example, a sampling rate of 10 kHz for power-frequency interference and 1 MHz for high-frequency interference. Data preprocessing includes applying a Hanning window to reduce spectral leakage; suppressing power-frequency interference with a 50 Hz to 60 Hz digital notch filter; and bandpass filtering with a third-order Butterworth filter set to a passband of 100 Hz to 100 kHz.

[0081] The electric field intensities in three orthogonal directions at each measurement location are combined to form orthogonal electric field intensity components. The specific implementation of this combination operation is as follows: Each measurement location generates three-dimensional electric field vector data with a timestamp, which is synchronized with the GPS clock. The three-dimensional electric field vector data structure includes the measurement location coordinates, field strength values ​​along the X-axis, the Y-axis, and the Z-axis, with the field strength values ​​expressed in volts per meter. The orthogonal electric field intensity components are stored in a two-dimensional array, where the array row index corresponds to the probe group number, the column index corresponds to the time series point, and each element is a three-dimensional field strength vector. The location coordinates are acquired using a GPS module with centimeter-level positioning accuracy. The GPS module is integrated with the three-dimensional electric field probe.

[0082] The control cable path is calibrated as follows: After the cable is laid, a laser rangefinder is used to map the spatial trajectory along the cable trench. The trajectory data is converted into a three-dimensional polyline in the geodetic coordinate system. The three-dimensional electric field probe must meet IP68 waterproofing requirements and operate within a temperature range of -40°C to +85°C. The sensitivity of the electric field sensor is regularly calibrated, for example, every six months using a standard field strength calibration device. Calibration points include 1 kV / m, 5 kV / m, and 10 kV / m. A calibration deviation exceeding ±1% triggers a sensor replacement procedure.

[0083] The dynamic adjustment mechanism for the preset safety threshold involves monitoring the cable insulation aging index. When the insulation resistance drops to 80% of its initial value, the preset safety threshold is lowered to 90% of its original value. If the local discharge exceeds 50 pico-cubic meters for 30 consecutive days, the preset safety threshold is lowered to 85% of its original value. Insulation resistance is measured using a 1000-volt megohmmeter with a measurement interval of seven days. Partial discharge monitoring uses a high-frequency current transformer with a sampling rate of 100 MHz.

[0084] Anti-interference measures for synchronous activation include: Manchester encoding for activation commands; a magnetic ring filter at the power controller input; and double-shielded twisted-pair probe power cables with a single-point grounding of the inner shield and multiple-point grounding of the outer shield. Temperature compensation during measurement involves a built-in temperature sensor in each electric field sensor, covering a temperature range of -40°C to +100°C. The temperature compensation coefficient is, for example, -0.2% per degree Celsius, and the compensation algorithm uses a polynomial fitting correction with a fitting order of 3.

[0085] Post-processing of the orthogonal electric field intensity components includes: outlier removal from the field intensity data in each direction, with the criterion being that five consecutive points deviate from the mean by more than 20%; filling missing data with cubic spline interpolation; and time alignment accuracy of the final output data within 1 microsecond. The operating status of all 3D electric field probes is monitored in real time: for example, overcurrent protection is triggered when current consumption exceeds 200 mA; and automatic range switching is initiated when the signal output amplitude reaches full scale 10 times in a row, with range switching time less than 100 microseconds.

[0086] The measurement data is verified by adding reference electric field probes at the beginning and end of the cable path. When the measured value at the same location deviates from the reference value by more than 5%, a probe self-test is initiated. This self-test checks the probe supply voltage fluctuation range, the sensor axial offset angle, and the signal transmission link attenuation. The signal transmission link attenuation test uses a 1 kHz sinusoidal signal injection with an attenuation tolerance of ±3 dB. The resulting orthogonal electric field strength component data packets are encapsulated every 100 milliseconds. The packet header contains the probe group number, sampling rate, range, and a checksum generated using a cyclic redundancy check.

[0087] S3. Detect the topological invariant distribution of the topologically ordered material on the surface of the control cable, and reconstruct the fiber bundle structure of the orthogonal electric field intensity components based on the gauge invariance mapping relationship between the topological invariant distribution and the orthogonal electric field intensity components. The specific implementation is as follows:

[0088] Angle-resolved photoelectron spectroscopy is used to scan the surface of the control cable shielding layer to obtain the electronic band structure of the topologically ordered material. The specific implementation of the scanning process includes: establishing a 10 mm × 10 mm grid partition on the surface of the shielding layer, and each grid center point is used as a scanning position; the scanning position spacing is set according to the grain size of the shielding layer, for example, when the grain size is less than 100 microns, the spacing is 0.5 mm, and when it is greater than 100 microns, the spacing is 1 mm. The excitation light source of the angle-resolved photoelectron spectroscopy uses a helium discharge lamp with a photon energy of 21.2 electron volts, a spot diameter of 0.2 mm, an incident angle adjustment range of 15 degrees to 75 degrees, and an angle step accuracy of 0.1 degree. The measurement parameters of the electronic band structure include: energy resolution of 10 millielectron volts, momentum resolution of 0.01 angstroms-1, and a data acquisition time of 50 milliseconds for each scanning point. The surface pretreatment of the shielding layer includes: ultrasonic cleaning with anhydrous ethanol for 5 minutes to remove surface contaminants; argon ion sputtering for 2 minutes to eliminate the oxide layer; maintaining a vacuum degree better than 1×10 -8 Pascal.

[0089] The spatial distribution parameters of the Chern number and Berry curvature are extracted from the electronic band structure as a topological invariant distribution. The extraction process is as follows: the band data at each scan position is partitioned into a Brillouin zone with a grid density of 100×100 points. The Chern number is calculated by integrating the Berry curvature over all discrete k-points in the zone multiplied by the area occupied by those k-points. The Berry curvature is calculated based on the anti-commutation relation of the gradient operator of the electron wave function, specifically by calculating the inner product differential of the conduction and valence band eigenstates. The spatial distribution parameters are generated by mapping the Chern number at each scan position to color depth and the Berry curvature value to contour density, forming a two-dimensional distribution map. The topological invariant distribution is stored as a floating-point matrix associated with spatial coordinates, with rows corresponding to the x-axis and columns corresponding to the y-axis. The element values ​​are normalized topological invariant strength values, normalized between 0 and 1.

[0090] A gauge invariance mapping relationship between the topological invariant distribution and the orthogonal electric field intensity components is established. The mapping relationship construction process includes: obtaining the orthogonal electric field intensity component data output from step S2, selecting a 1-second data window synchronized with the photoelectron spectrum scan; inputting the topological invariant distribution parameters and the orthogonal electric field intensity components into a tensor regression model. The mathematical form of the tensor regression model is expressed as a linear transformation relationship between the topological invariant tensor and the electric field intensity tensor. The specific parameters of the gauge invariance mapping are determined by fitting the transformation coefficient matrix using the least squares method, with the fitting objective function set to minimize the covariant derivatives of the transformed electric field intensity components under the gauge transformation; the covariant derivatives are calculated using the Riemannian geometry connection form, and the connection coefficient value range is set to -0.5 to +0.5. The mapping relationship is verified by performing a comparative test on the surface of a reference sample with known topological order, requiring that the deviation of the mapped electric field direction be less than 0.5 degrees.

[0091] The spatial vector directions of the orthogonal electric field intensity components are corrected according to the gauge invariance mapping relationship to form a fiber bundle structure of the orthogonal electric field intensity components. The correction operation is technically implemented by applying a rotation transformation to the orthogonal electric field intensity component vectors at each measurement location. The rotation matrix elements are derived from the coefficient matrix of the gauge invariance mapping relationship. The iterative condition for the rotation transformation is that the direction difference between adjacent position vectors is less than 1 degree, and the maximum number of iterations is limited to 100. The fiber bundle structure formation process includes: establishing a three-dimensional manifold coordinate system for the cable path; assigning the corrected electric field vector to each point on the manifold; connecting adjacent point vectors using the parallel translation rule, with the parallel translation connection coefficient being the connection coefficient value in the gauge invariance mapping. The final output fiber bundle structure data contains three parameters: spatial position, the direction angle of the corrected electric field vector, and the connection coefficient value. The data format is a time-space four-dimensional array.

[0092] A laser tracker is used as the positioning reference for scanning the cable shield surface, achieving a positioning accuracy of 5 microns. The temperature compensation scheme for the electronic band structure involves integrating a thermoelectric cooler into the spectrometer sample stage, with a temperature control range of -10°C to +50°C. The temperature drift compensation coefficient is, for example, -0.5 parts per million per degree Celsius. The topological invariant distribution is updated by triggering a local rescan when the cable bend radius changes by more than 10%. The rescanned area is the bending stress concentration zone, with a radius of three times the cable diameter.

[0093] The dynamic adjustment of the gauge invariance mapping relationship is based on monitoring the phase transition characteristics of topologically ordered matter. When the average Chern number changes by more than 0.1, the mapping coefficients are refitted. When the ambient humidity exceeds 80% for 24 consecutive hours, a humidity correction factor is added to the mapping coefficients. The correction factor is calculated as the relative humidity multiplied by 0.0001. A visual verification method for the fiber bundle structure involves attaching fluorescent microsphere markers to the cable surface; capturing the microsphere displacement with a high-speed camera at a resolution of 0.1 micron; and comparing the mechanical displacement vector with the electric field vector direction. A deviation exceeding 2 degrees triggers a recheck of the mapping relationship.

[0094] All data processing hardware utilizes an embedded graphics processor with a floating-point computing capability exceeding 1 trillion operations per second. Noise suppression measures for the electronic band structure include five repeated acquisitions at each scan point and averaging. A wavelet threshold denoising algorithm is applied, using the DB4 wavelet basis and a threshold set at three times the noise standard deviation. The resulting fiber bundle structure data is updated every 200 milliseconds, and data packets are verified using a 32-bit cyclic redundancy check (CRC) with the check polynomial 0x04C11DB7.

[0095] S4. Generate the common-mode interference coupling coefficient based on the spatial vector relationship between the ground grid potential gradient distribution direction and the reconstructed orthogonal electric field strength components. The specific implementation is as follows:

[0096] Obtain the unit direction vector corresponding to the direction of the ground grid potential gradient distribution. The unit direction vector generation process includes: receiving the ground grid potential gradient distribution direction data output from step S1, which is the angle value with the positive direction of the X-axis of the ground grid plane; establishing a two-dimensional rectangular coordinate system on the ground grid plane, with the origin set at the main grounding pile of the substation, the positive direction of the X-axis pointing due north, and the positive direction of the Y-axis pointing due east; calculating the X and Y components of the direction vector based on the angle value, with the X component equal to the cosine value of the angle and the Y component equal to the sine value of the angle; and normalizing the modulus of the unit direction vector by dividing the X and Y components by the vector modulus, which is the square root of the sum of the squared X and Y components. The normalized unit direction vector is stored as a two-dimensional floating-point array containing a timestamp, with the array elements in the order [X component value, Y component value] and a timestamp accuracy of 1 millisecond.

[0097] Extract the electric field vectors projected on the ground grid plane by reconstructing the orthogonal electric field intensity components. The technical implementation of this extraction operation includes: obtaining the fiber bundle structure data of the orthogonal electric field intensity components output in step S3, which includes the spatial position and the corrected electric field vector direction angle; establishing a ground grid plane projection coordinate system with the Z axis perpendicular to the ground plane and the X and Y axes defined consistent with the unit direction vector coordinate system; decomposing the three-dimensional electric field vector into the projection coordinate system, with the X and Y components of the electric field vector directly used as the projection components and the Z component set to zero; calculating the modulus of the projected electric field vector as the square root of the sum of the squares of the X and Y components. The electric field vector is stored in a three-dimensional array associated with the spatial position. The array dimensions include the X coordinate, the Y coordinate, and the time point, with each element being [X component value, Y component value, modulus value].

[0098] Calculate the directional angle between the unit direction vector and the electric field vector. The specific method for calculating the directional angle is as follows: perform a dot product operation on the unit direction vector and the electric field vector at the same time and spatial position. The dot product result is equal to the X component of the unit direction vector multiplied by the X component of the electric field vector plus the Y component of the unit direction vector multiplied by the Y component of the electric field vector; divide the dot product result by the modulus of the electric field vector to obtain the cosine value; calculate the radian value of the angle using the inverse cosine function, and then convert it into an angle value. The calculation constraints of the angle value include: when the modulus of the electric field vector is less than 0.1 volts per meter, the angle value is set to zero; when the dot product result exceeds the range of negative 1 to positive 1, the nearest valid value is used instead. The output resolution of the directional angle data is 0.1 degrees, and the storage format is a time-space three-dimensional floating-point matrix.

[0099] The common-mode interference coupling coefficient is generated based on the product of the directional angle and the modulus of the electric field vector. The specific implementation of this product relationship is as follows: the common-mode interference coupling coefficient is equal to the directional angle multiplied by the modulus of the electric field vector, multiplied by a proportional coefficient. The proportional coefficient is set based on the transfer impedance of the cable shield and ranges from 0.01 to 0.05. The specific value is determined through calibration tests: for example, if a 10-ampere interference current is injected into the grounding grid and the cable induced voltage is measured, the proportional coefficient is equal to the induced voltage divided by the injected current, divided by the product of the directional angle and the modulus of the field strength. The common-mode interference coupling coefficient is measured in volts per ampere, and the output data format is a one-dimensional array of time series, where the array index corresponds to a time point and the element value is a floating-point coupling coefficient value.

[0100] The grounding grid's plane coordinate system is calibrated annually using a total station to measure the main grounding stake locations. The coordinate system origin is updated if the coordinate deviation exceeds 5 cm. Temperature drift compensation for unit direction vectors involves integrating a temperature sensor into the magnetic induction probe. The temperature compensation coefficient, for example, is negative 10 parts per million per degree Celsius, and the compensation amount is added to the angle measurement. The exception handling mechanism for electric field vector projection includes the following: If the projected vector modulus is less than 5% of the original modulus, the projection is deemed invalid, triggering step S3 data review. If the modulus values ​​of 10 consecutive sampling points at the same location exceed the allowable error range, the system automatically switches to the backup electric field probe data.

[0101] The iterative optimization process for directional angle calculation is as follows: when the rate of change of the angle between adjacent time points exceeds 100 degrees per second, cubic spline interpolation smoothing is initiated. The maximum allowable rate of change threshold is set based on the cable length, for example, 50 degrees per second for a 100-meter cable and 30 degrees per second for a 200-meter cable. Dynamic correction of the common-mode interference coupling coefficient involves multiplying the coupling coefficient by a humidity correction factor, such as 1.05, when the ambient humidity exceeds 90%; and by a temperature correction factor, such as 0.95, when the cable temperature exceeds 70°C. This correction factor is acquired in real time by a temperature and humidity sensor installed at the cable connector.

[0102] The data verification method involves connecting a standard current transformer in series between the ground grid and the cable. The measured common-mode current is compared with the theoretical coupling coefficient, which is equal to the coupling coefficient multiplied by the ground grid current. Any deviation exceeding 10% triggers coefficient recalibration. All output data is transmitted in packets every 50 milliseconds. The packet header contains a checksum sequence number, data length, and version number. The data field stores the coupling coefficient array, stored in a low-order byte-first format. Ferroelectric memory is used as the storage medium, and data retention is at least 10 years.

[0103] The threshold for the common-mode interference coupling coefficient is set as follows: when the coefficient value exceeds 0.5 volts per ampere for 100 milliseconds, step S5 is triggered; when the coefficient value exceeds 1.0 volts per ampere, fault recording is initiated. The coefficient display resolution is set to 0.001 volts per ampere, with a display update frequency of 10 times per second. Historical data is stored using a circular cache mechanism, with a cache depth of the most recent 24 hours and a storage interval of 10 milliseconds.

[0104] S5. Determine the electrostrictive tensor of the relay insulation medium based on the common-mode interference coupling coefficient, and generate a dynamic compensation voltage command based on the intrinsic relationship between strain and electric field in the inverse piezoelectric effect. The specific implementation is as follows:

[0105] The electrostrictive tensor components are determined based on the correspondence between the common-mode interference coupling coefficient and the material parameters of the relay insulation dielectric. This correspondence is established by pre-storing a mapping table of electrostrictive parameters for different insulation materials, obtained through material calibration testing; receiving the common-mode interference coupling coefficient output from step S4, which is a floating-point array of time series; inputting the coupling coefficient into the material parameter mapping table, where the index dimension of the mapping table includes the coupling coefficient value range and the temperature value range; the output of the electrostrictive tensor components is a 3-row, 3-column symmetric matrix, where the matrix elements represent the electrostrictive coefficients in different directions, all in units of square meters per volt squared. The specific method for the material calibration test is as follows: preparing a standard specimen with dimensions of, for example, 10 mm × 10 mm × 1 mm; applying a stepped electric field from 0 to 10 kilovolts per millimeter on both sides of the specimen, with a step size of, for example, 1 kilovolt per millimeter; and measuring the strain in the specimen's thickness direction using a laser interferometer. The electrostrictive coefficient is equal to the strain value divided by the square of the electric field strength. The temperature range covers -40 degrees Celsius to +150 degrees Celsius, and the temperature data is derived from the relay housing temperature sensor.

[0106] The strain distribution of the relay's insulation under common-mode interference is calculated using the electrostrictive tensor components. The strain distribution calculation process involves establishing a three-dimensional finite element model of the relay's insulation with a mesh size no larger than 0.1 mm. A common-mode interference electric field is applied to the model surface, with the electric field strength equal to the common-mode interference coupling coefficient multiplied by the grounding grid fault current value; the fault current value is derived from grounding grid fault waveform data. The strain tensor is calculated by multiplying the electrostrictive tensor components by the electric field strength components, and then by the electric field strength components again. The result is a six-component strain tensor. The strain distribution is stored as a three-dimensional array associated with spatial coordinates. The array elements include the six strain component values: εxx, εyy, εzz, εxy, εyz, and εzx. The strain values ​​are expressed in microstrain units. Boundary conditions are set as zero strain in the relay's metal contact region and zero stress on the insulating medium's free surface.

[0107] Based on the intrinsic relationship between strain and electric field in the inverse piezoelectric effect, the strain distribution is converted into a compensation electric field intensity distribution. The technical implementation of this conversion operation involves directly converting the strain state at each point within the relay's insulating medium into the compensation electric field intensity value at the corresponding spatial location through the linear constitutive relationship between the strain tensor and electric field intensity in the inverse piezoelectric effect. The mathematical form of this constitutive relationship states that the electric field intensity component is equal to the inverse of the electrostrictive coefficient matrix multiplied by the strain tensor component. The electrostrictive coefficient matrix is ​​a 6-row, 3-column matrix obtained from the material mapping table. The compensation electric field intensity value is calculated by performing matrix multiplication on the six strain components at each grid point, outputting three electric field intensity components: Ex, Ey, and Ez. The spatial resolution of the compensation electric field intensity distribution is 0.1 mm, and the field strength is measured in volts per millimeter. The conversion relationship is verified by ensuring that the deviation between the measured electric field intensity and the calculated value is less than 5% on a standard specimen with a known strain distribution.

[0108] A dynamic compensation voltage command is generated based on the integration of the compensation electric field intensity distribution along the relay contact spacing. The specific steps of the integration operation include: determining the spatial path in the direction of the relay contact spacing, which is the line connecting the centers of the moving and static contacts; performing a line integration of the tangential component of the compensation electric field intensity along the path, with an integration step of 0.01 mm; and expressing the integration formula as discretizing the path into multiple points, multiplying the tangential component of the electric field at each point by the step size and then accumulating them. The logic for generating the dynamic compensation voltage command is as follows: the integration result is the compensation voltage amplitude; the voltage command waveform is dynamically adjusted based on the fault current change rate: for example, when the current change rate is greater than 1 kiloamperes per microsecond, a rectangular wave with a rising edge of 1 microsecond is used; when it is less than 1 kiloamperes per microsecond, a trapezoidal wave with a rising edge of 10 microseconds is used. The output amplitude range of the voltage command covers negative 1000 volts to positive 1000 volts, with a resolution of 0.1 volt.

[0109] The three-dimensional model of the relay's insulation dielectric was constructed based on the actual relay's internal structure captured via industrial computed tomography (CT) scanning with a resolution of 50 microns. Model material parameters included a relative permittivity of 3.0 to 5.0 and a conductivity of 10-15 Siemens per meter to 10-12 Siemens per meter. The iterative convergence criteria for the strain distribution calculation were that the strain change between iterations be less than 0.01%, with a maximum number of iterations of 100. The temperature compensation scheme for the electric field intensity distribution corrects the strain value based on the material's thermal expansion coefficient. For example, for epoxy resin, the correction factor is 50 microstrain per degree Celsius, and this correction is added to the strain tensor components.

[0110] Safety limits for dynamic compensation voltage commands include: the maximum output amplitude must not exceed 80% of the relay's insulation withstand voltage; and the trigger path must be recalibrated if the contact spacing varies by more than 5%. The command waveform is generated using a field-programmable gate array (FPGA) with a 100 MHz clock frequency. The data verification mechanism involves connecting a standard voltage probe in parallel with the relay's auxiliary contacts; and a trigger coefficient matrix review when the command voltage deviates from the measured voltage by more than 3%. The final dynamic compensation voltage command data packet contains four parameters: timestamp, voltage amplitude, waveform type, and rise time. The transmission protocol uses a controller area network bus with a baud rate of 500 kilobits per second.

[0111] The electrostrictive coefficient matrix is ​​stored in read-only memory by pre-storing typical material parameters for three types of materials, including alumina ceramic, epoxy resin, and silicone rubber. When new materials are used, new parameters are programmed via the serial peripheral interface. The conversion of strain distribution to electric field distribution is accelerated by using parallel computing on a graphics processor, with each thread processing one grid point and a thread block size of 16×16. The adaptive adjustment mechanism for the integration path automatically extends the path length when contact wear increases the spacing. This extension is measured using a contact displacement sensor with a resolution of 0.01 mm. The dynamic compensation voltage command is filtered using a second-order infinite impulse response filter with a cutoff frequency set to one-tenth the switching frequency.

[0112] S6: Superimpose the dynamic compensation voltage command on the power switching control circuit to drive the standby power switching actuator. The specific implementation is as follows:

[0113] Acquire the voltage amplitude and timing waveform of the dynamic compensation voltage instruction. This acquisition process includes receiving the dynamic compensation voltage instruction data packet output in step S5. The data packet contains a timestamp, voltage amplitude, waveform type, and rising edge time parameters. The voltage amplitude range is negative 1000 volts to positive 1000 volts, with a resolution of 0.1 volt. The timing waveform reconstruction method generates a corresponding function curve based on the waveform type parameters: for example, the rectangular wave function linearly increases the voltage value from 0 to the target amplitude within the rising edge time, and the trapezoidal wave function increases the platform holding time after the rising edge, such as 10 microseconds. The waveform data is stored in the form of an array of time-voltage value pairs with a time resolution of 0.1 microseconds. The array length is determined by the instruction duration. For example, a duration of 20 microseconds corresponds to 200 data points.

[0114] The dynamic compensation voltage command is coupled to the control signal transmission line of the power switching control loop via an isolation amplifier. Technical specifications for the isolation amplifier include a voltage gain of 1.0±0.1%, a DC bandwidth of 10 MHz, and an isolation withstand voltage of 5000 V RMS. The coupling operation is implemented as follows: the isolation amplifier input port is connected to the dynamic compensation voltage command output port, and the output port is connected to the control signal transmission line through a 100-ohm resistor in series. The coupling point is located between the main controller output and the power driver input, no more than 0.5 meters from the power driver input. Interference prevention measures include installing a ferrite ring at the coupling point; using a twisted-pair shielded transmission line with a single-point grounding of the shield; and adding a π-type filter with a cutoff frequency of 1 MHz to the isolation amplifier power supply.

[0115] During the relay coil excitation time window, the coupled dynamic compensation voltage command is injected into the power switching control loop. The excitation time window is determined by monitoring the voltage across the relay coil. The window is considered open when the voltage exceeds 10% of the coil's rated voltage, and closed when it falls below 5%. The injection logic includes real-time monitoring of the excitation time window status; closing the injection switch (using a photo-controlled thyristor with a conduction time of less than 100 nanoseconds) when the window is open; and opening the injection switch when the window is closed. The injection signal amplitude is calibrated by connecting a precision current transformer in series with the injection loop, with a transformer ratio of 1000:1. The isolation amplifier gain is automatically adjusted when the injected current deviates by more than 3% from the converted command voltage.

[0116] The injected drive signal from the power switching control circuit triggers the actuating coil of the backup power supply switching actuator. The trigger control is implemented as follows: the drive signal is input to a power driver, which utilizes an insulated gate bipolar transistor half-bridge circuit with a switching frequency of 20 kHz. The trigger current threshold of the actuating coil is set to 0.5 amps. When the drive signal current exceeds the threshold for 10 microseconds, the actuator armature engages. The protection mechanism includes a freewheeling diode connected in parallel across the actuating coil; an overcurrent protection circuit with a threshold of 2.5 amps and a response time of 1 microsecond; and air cooling activated when the coil temperature rises above 50 degrees Celsius.

[0117] The method for compensating for transmission delays in dynamically compensated voltage commands involves measuring the transmission time from command generation to injection, for example by comparing the waveforms at the command source and injection point using an oscilloscope. This delay is then pre-compensated in the command generation timestamp, with a compensation accuracy of 0.1 microsecond. Regular calibration of the isolation amplifier is performed every three months using a standard voltage source input. The output deviation must be less than ±0.5%. Otherwise, the amplifier module must be replaced. Anomaly detection in the excitation time window: When the window opening time exceeds 150% of the relay's standard pull-in time, a mechanical jam is detected, triggering an alarm signal.

[0118] Feedback verification of the backup power supply switching actuator: Hall effect sensors are installed on the actuator's moving parts to detect displacement, for example, by converting changes in magnetic field strength. If the displacement does not reach 90% of the set stroke within 5 milliseconds, a secondary trigger is initiated. The secondary trigger strategy increases the compensation voltage amplitude by 20% and extends the pulse width to 15 microseconds. After three consecutive trigger failures, the system is locked. Electrical isolation requirements for all control circuits include: insulation resistance between inputs and outputs greater than 100 megohms, and a power frequency withstand voltage of 4000 volts for one minute without breakdown.

[0119] Actuating coil drive energy management: A 1000 microfarad energy storage capacitor bank is installed; when the main power supply voltage drops by more than 20%, the capacitor power supply is automatically switched. Actuator position retention mechanism: After energization, the actuator switches to a holding current, which is 30% of the trigger current and is adjusted via pulse width modulation. Historical operation data recording: The command waveforms, drive current curves, and execution time parameters for the last 100 switching operations are stored in a binary file format with a file size not exceeding 1 megabyte.

[0120] System self-test process: Upon power-up, a test pulse is automatically injected with a pulse amplitude of 50 volts and a duration of 5 microseconds. The injected circuit current response is monitored, and the response amplitude should be between 0.45 amps and 0.55 amps. If it exceeds this tolerance, a fault code is generated. Fault code classifications include: E01 for an open injection path, E02 for a gain error, and E03 for a time window out of sync. A maintenance interface is reserved: real-time parameters can be read via the serial communication port, using Modbus RTU protocol and a baud rate of 19200 bits per second.

[0121] Example 2: Figure 2 A schematic structural diagram of a drive power supply failure switching system according to the present invention is provided. The drive power supply failure switching system comprises:

[0122] Gradient monitoring module, used to collect the ground grid potential gradient amplitude and distribution direction in real time when the ground grid fails;

[0123] The electric field measurement module is used to synchronously measure the orthogonal electric field intensity components on the control cable path when the grid potential gradient amplitude exceeds a preset safety threshold;

[0124] A topology reconstruction module is used to detect the topological invariant distribution of the topologically ordered material on the surface of the control cable and reconstruct the fiber bundle structure of the orthogonal electric field intensity components based on the gauge invariance mapping relationship between the topological invariant distribution and the orthogonal electric field intensity components;

[0125] A coupling generation module is used to generate a common-mode interference coupling coefficient based on the spatial vector relationship between the ground grid potential gradient distribution direction and the reconstructed orthogonal electric field strength components;

[0126] A voltage generation module is used to determine the electrostrictive tensor of the relay insulation medium based on the common-mode interference coupling coefficient, and to generate a dynamic compensation voltage command through the intrinsic relationship between strain and electric field in the inverse piezoelectric effect;

[0127] The switching drive module is used to superimpose the dynamic compensation voltage instruction on the power switching control loop to drive the backup power switching actuator.

[0128] The calculations involved in the embodiments are all dimensionless numerical calculations, and the preset parameters and thresholds in the calculations are set by those skilled in the art according to actual conditions.

[0129] It should be noted that the present invention can be deployed on the device itself to realize embedded applications, and can also be run on a PC or other terminal with a user interface, thereby meeting various hardware environments and usage requirements.

[0130] The above embodiments can be implemented in whole or in part through software, hardware, firmware, or any other combination. When implemented using software, the above embodiments can be implemented in whole or in part in the form of a computer program product. The computer program product includes one or more computer instructions or computer programs. When the computer instructions or computer program are loaded or executed on a computer, the processes or functions described in the embodiments of the present application are generated in whole or in part. The computer can be a general-purpose computer, a special-purpose computer, a computer network, or other programmable device. The computer instructions can be stored in a computer-readable storage medium or transmitted from one computer-readable storage medium to another. For example, the computer instructions can be transmitted from one website, computer, server, or data center to another website, computer, server, or data center via wireless or wired transmission methods; wired transmission methods include optical fiber, twisted pair, coaxial cable, etc.; wireless transmission methods include infrared, microwave, etc. The computer-readable storage medium can be any available medium that can be accessed by a computer or a data storage device such as a server or data center that contains a collection of one or more available media. The available medium can be a magnetic medium (e.g., a floppy disk, hard disk, tape), an optical medium (e.g., a DVD), or a semiconductor medium. The semiconductor medium can be a solid-state drive.

[0131] Those skilled in the art will clearly understand that, for the convenience and brevity of description, the specific working processes of the systems, devices and modules described above can refer to the corresponding processes in the aforementioned method embodiments and will not be repeated here.

[0132] In the several embodiments provided in this application, it should be understood that the disclosed systems, devices and methods can be implemented in other ways. For example, the device embodiments described above are merely schematic. For example, the division of the modules is only a logical function division. In actual implementation, there may be other division methods, such as multiple modules or components can be combined or integrated into another system, or some features can be ignored or not executed. Another point is that the mutual coupling or direct coupling or communication connection shown or discussed can be through some interfaces, indirect coupling or communication connection of devices or modules, which can be electrical, mechanical or other forms.

[0133] The modules described as separate components may or may not be physically separate, and the components shown as modules may or may not be physical modules, and may be located in one place or distributed across multiple network modules. Some or all of the modules may be selected to achieve the purpose of this embodiment according to actual needs.

[0134] In addition, each functional module in each embodiment of the present application may be integrated into one processing module, or each module may exist physically separately, or two or more modules may be integrated into one module.

[0135] If the functions are implemented in the form of software function modules and sold or used as independent products, they can be stored in a computer-readable storage medium. Based on this understanding, the technical solution of the present application, or the part that contributes to the prior art, or the part of the technical solution, can be embodied in the form of a software product. The computer software product is stored in a storage medium and includes several instructions for enabling a computer device (which can be a personal computer, server or network device, etc.) to execute all or part of the steps of the method described in each embodiment of the present application. The aforementioned storage medium includes various media that can store program codes, such as a USB flash drive, a mobile hard disk, a read-only memory (ROM), a random access memory (RAM), a magnetic disk or an optical disk.

[0136] The above description is merely a specific embodiment of the present application, but the scope of protection of the present application is not limited thereto. Any changes or substitutions that can be easily conceived by a person skilled in the art within the technical scope disclosed in this application should be included in the scope of protection of the present application. Therefore, the scope of protection of the present application should be based on the scope of protection of the claims.

[0137] Finally: The above description is only a preferred embodiment of the present invention and is not intended to limit the present invention. Any modifications, equivalent substitutions, improvements, etc. made within the spirit and principles of the present invention should be included in the scope of protection of the present invention.

Claims

1. A driving power supply failure switching method, characterized in that: include: S1, real-time acquisition of ground grid potential gradient amplitude and distribution direction when the ground grid fails; S2. When the grid potential gradient amplitude exceeds a preset safety threshold, synchronously measure the orthogonal electric field intensity components on the control cable path; S3, detecting the topological invariant distribution of the topologically ordered material on the surface of the control cable, and reconstructing the fiber bundle structure of the orthogonal electric field intensity components based on the gauge invariance mapping relationship between the topological invariant distribution and the orthogonal electric field intensity components; S4. Generate a common-mode interference coupling coefficient based on the spatial vector relationship between the ground grid potential gradient distribution direction and the reconstructed orthogonal electric field strength components; S5. Determine the electrostrictive tensor of the relay insulation medium according to the common-mode interference coupling coefficient, and generate a dynamic compensation voltage command through the intrinsic relationship between strain and electric field in the inverse piezoelectric effect; S6. Superimpose the dynamic compensation voltage instruction on the power supply switching control circuit to drive the standby power supply switching actuator.

2. The driving power supply failure switching method according to claim 1, characterized in that: Real-time acquisition of ground grid potential gradient amplitude and distribution direction during ground grid faults, including: Deploy an array of magnetic induction probes at the intersection of ground grid conductors; The direction of the transient magnetic field generated by the fault current is synchronously measured by an array of magnetic induction probes; According to the spatial correlation between the transient magnetic field direction and the geometric structure of the grounding grid conductor, the grounding grid potential gradient amplitude and grounding grid potential gradient distribution direction are generated.

3. The driving power supply failure switching method according to claim 2, characterized in that: The distribution density of the magnetic induction probe array is positively correlated with the conductor crossing complexity.

4. The driving power supply failure switching method according to claim 1, characterized in that: When the grid potential gradient amplitude exceeds the preset safety threshold, the orthogonal electric field strength components on the control cable path are measured synchronously, including: Multiple groups of three-dimensional electric field probes are set on the control cable path, and each group of three-dimensional electric field probes includes three mutually perpendicular electric field sensors; When the grid potential gradient amplitude exceeds the preset safety threshold, all three-dimensional electric field probes are activated simultaneously; The three mutually perpendicular electric field sensors of each set of three-dimensional electric field probes are used to measure the electric field strength in three orthogonal directions at corresponding positions on the control cable path; The electric field intensities in three orthogonal directions at each measurement position are combined to form orthogonal electric field intensity components.

5. The driving power supply failure switching method according to claim 1, characterized in that: The topological invariant distribution of the topologically ordered material on the surface of the control cable is detected, and the fiber bundle structure of the orthogonal electric field intensity components is reconstructed based on the gauge invariance mapping relationship between the topological invariant distribution and the orthogonal electric field intensity components, including: Angle-resolved photoelectron spectroscopy is used to scan the surface of the control cable shield to obtain the electronic band structure of topologically ordered materials. The spatial distribution parameters of Chern number and Berry curvature are extracted from the electronic band structure as topological invariant distribution; Establish the gauge invariance mapping relationship between the topological invariant distribution and the orthogonal electric field intensity components; The spatial vector directions of the orthogonal electric field intensity components are corrected according to the gauge invariance mapping relationship to form a fiber bundle structure of the orthogonal electric field intensity components.

6. The driving power supply failure switching method according to claim 1, characterized in that: Based on the spatial vector relationship between the ground grid potential gradient distribution direction and the reconstructed orthogonal electric field strength components, the common mode interference coupling coefficient is generated, including: Obtain the unit direction vector corresponding to the ground grid potential gradient distribution direction; Extract the electric field vector of the reconstructed orthogonal electric field intensity component projected on the grounding grid plane; Calculate the angle between the unit direction vector and the electric field vector; The common-mode interference coupling coefficient is generated according to the product relationship between the direction angle and the electric field vector modulus.

7. The driving power supply failure switching method according to claim 1, characterized in that: The electrostrictive tensor of the relay insulation medium is determined based on the common-mode interference coupling coefficient, and a dynamic compensation voltage command is generated through the intrinsic relationship between strain and electric field in the inverse piezoelectric effect, including: According to the corresponding relationship between the common mode interference coupling coefficient and the parameters of the relay insulation medium material, the electrostrictive tensor component is determined; Calculate the strain distribution of relay insulation under common mode interference through electrostrictive tensor components; According to the intrinsic relationship between strain and electric field in the inverse piezoelectric effect, the strain distribution is converted into the compensation electric field intensity distribution; A dynamic compensation voltage command is generated based on the integration of the compensation electric field intensity distribution along the relay contact spacing direction.

8. The driving power supply failure switching method according to claim 7, characterized in that: According to the intrinsic relationship between strain and electric field in the inverse piezoelectric effect, the strain distribution is converted into the compensation electric field intensity distribution, which includes: Through the linear constitutive relationship between strain tensor and electric field intensity in the inverse piezoelectric effect, the strain state of each point inside the relay insulation medium is directly converted into the compensation electric field intensity value at the corresponding spatial position; The strain tensor component and the electric field intensity component establish a conversion relationship through the electrostrictive coefficient matrix to form a spatial mapping of the compensation electric field intensity distribution.

9. The driving power supply failure switching method according to claim 1, characterized in that: The dynamic compensation voltage command is superimposed on the power switching control loop to drive the backup power switching actuator, including: Obtaining the voltage amplitude and timing waveform of the dynamic compensation voltage instruction; coupling the dynamic compensation voltage command to the control signal transmission line of the power switching control loop through an isolation amplifier; In the relay coil excitation time window, the coupled dynamic compensation voltage command is injected into the power switching control loop; According to the injected power switching control circuit driving signal, the action coil of the standby power switching actuator is triggered.

10. A driving power supply failure switching system, used to implement the driving power supply failure switching method according to any one of claims 1 to 9, characterized in that: include: Gradient monitoring module, used to collect the ground grid potential gradient amplitude and distribution direction in real time when the ground grid fails; The electric field measurement module is used to synchronously measure the orthogonal electric field intensity components on the control cable path when the grid potential gradient amplitude exceeds a preset safety threshold; A topology reconstruction module is used to detect the topological invariant distribution of the topologically ordered material on the surface of the control cable and reconstruct the fiber bundle structure of the orthogonal electric field intensity components based on the gauge invariance mapping relationship between the topological invariant distribution and the orthogonal electric field intensity components; A coupling generation module is used to generate a common-mode interference coupling coefficient based on the spatial vector relationship between the ground grid potential gradient distribution direction and the reconstructed orthogonal electric field strength components; A voltage generation module is used to determine the electrostrictive tensor of the relay insulation medium based on the common-mode interference coupling coefficient, and to generate a dynamic compensation voltage command through the intrinsic relationship between strain and electric field in the inverse piezoelectric effect; The switching drive module is used to superimpose the dynamic compensation voltage instruction on the power switching control loop to drive the backup power switching actuator.

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