Composite vibration reduction cutter handle filled with metal-high polymer material and design method of composite vibration reduction cutter handle

Abstract

According to the composite vibration reduction cutter handle filled with the metal-high polymer materials and the design method of the composite vibration reduction cutter handle, a composite structure is introduced on the basis of a common large-feed milling cutter handle, the use rigidity of the cutter handle is guaranteed, meanwhile, damping of the cutter handle is improved, and forced vibration extremely prone to occurring in the large-feed milling process of the cutter handle is reduced. The damping performance of a composite structure formed by filling metal pores with a high polymer material is researched, damping optimization design of the composite structure under a specific working condition is achieved, finally the composite structure is filled into a cavity of the cutter handle, the damping of the cutter handle is improved while the rigidity is guaranteed, and therefore the purpose of improving the machining efficiency and the machining quality is achieved.

Description

Technical Field

[0001] The present invention relates to the technical field of intelligent manufacturing equipment, in particular to an intelligent metal cutting technology, and in particular to a composite vibration-damping tool holder filled with metal-polymer materials and a design method thereof. Background Art

[0002] In recent years, high-speed and high-efficiency machining technology has developed rapidly in the field of mechanical machining due to its high efficiency, high quality and low energy consumption, and is widely used in fields such as aerospace. For difficult-to-machine materials, such as titanium alloys, the difficulty in machining lies in low thermal conductivity and work hardening, which limits the efficiency of traditional milling. Therefore, high-feed milling methods have emerged, which can achieve efficient machining on lower-power machine tools, especially when processing large-sized, thin-walled, and complex-structured titanium alloy structural parts. The research and development of high-feed milling cutters has become the key to improving machining levels. It can deal with vibration, low efficiency, tool wear and surface quality problems that occur during the cutting process of difficult-to-machine materials such as titanium alloys, thereby significantly improving the level of cutting machining technology in the aerospace field.

[0003] In the existing technology, the friction damping principle is applied in the design of vibration-damping milling cutter rods, which increases the maximum axial cutting depth of the vibration-damping milling cutter rods compared with ordinary milling cutter rods of the same size. However, the friction damper has very high requirements on the wear resistance of the material and reduces the stiffness and service life of the milling cutter rod to a certain extent.

[0004] Prior art has created impact energy dampers by filling the tool cavity with powder particles. Orthogonal experiments have been conducted to study the effects of key filling parameters (particle density, particle diameter, and particle filling ratio) on cutting performance. The optimal parameter combination has been identified, improving machining quality. However, particle damping devices can suffer from particle accumulation, which can affect their damping effectiveness and reduce their performance to a certain extent.

[0005] The tool design method disclosed in Chinese patent No. 202310390928.4 changes the tool structural parameters to make the tool frequency consistent with the natural frequency of the machine tool spindle, thereby reducing the frequency response at the tool tip and improving cutting stability.

[0006] Although the above existing technologies have achieved tool vibration reduction to a certain extent and improved processing quality, there are still problems such as shortened tool life and poor tool applicability. Summary of the Invention

[0007] In response to the above-mentioned problems in the prior art, the present application proposes a composite vibration-damping tool holder filled with metal-polymer material, which includes a metal structure, a polymer material, a torque groove and a basic tool holder; the polymer material fills the pores of the metal structure to form a metal-polymer composite structure; the torque groove is located between the metal-polymer composite structure and the basic tool holder.

[0008] In one embodiment, the metal structure includes a plurality of metal units, each of which includes a plurality of inclined beams having a common end point and a plurality of straight beams for connecting the other ends of the inclined beams.

[0009] In one embodiment, the common endpoint is replaced by a regular hexahedron structure composed of a plurality of metal beams.

[0010] In one embodiment, the metal structure includes a plurality of metal units, each metal unit includes a plurality of straight beams parallel to each other, and adjacent straight beams are connected by crossed oblique beams.

[0011] In one embodiment, the metal material is stainless steel.

[0012] In one embodiment, the polymer material is polyurethane, epoxy resin or silicone rubber.

[0013] The present application also relates to a design method for a composite vibration-damping toolholder filled with metal-polymer materials, comprising:

[0014] Step 1: Perform cyclic tensile tests on samples of different configurations and different polymer material combinations to obtain their hysteresis curves and calculate their respective damping loss factors, and select the configuration and polymer material combination with the highest damping loss factor;

[0015] Step 2: Perform uniaxial compression and stress relaxation tests on the polymer material to obtain its hyperelastic and viscoelastic material parameters;

[0016] Step 3: Establish a finite element model of the metal-polymer composite unit and perform compression simulation and stress relaxation simulation on it;

[0017] Step 4: Input the material parameters obtained in step 2, obtain its force-displacement curve, and obtain the linear elastic and viscoelastic material parameters of the composite element;

[0018] Step 5: Establish a finite element model corresponding to the cyclic tensile test, input the material parameters obtained in step 4, set the sinusoidal displacement control, and output the corresponding hysteresis curve;

[0019] Step 6: Based on the combination of the configuration with the maximum damping loss factor obtained in step 1 and the polymer material, the finite element process of steps 2 to 6 is used to obtain multiple sets of different hysteresis curves;

[0020] Step 7: Establish the hysteresis curve nonlinear dynamic model of the composite unit:

[0021]

[0022] Where F is the restoring force, X is the deformation of the composite element, is the velocity of the composite unit, K1, K2, and K3 are the first-order nonlinear elastic force coefficient, the second-order elastic force coefficient, and the third-order elastic force coefficient, respectively; C1 is the linear damping term coefficient, and C2 is the nonlinear damping term coefficient;

[0023] Step 8: Decompose the hysteresis curve into nonlinear elastic force and nonlinear damping force;

[0024] Nonlinear elastic force:

[0025] F k (X) = K1X + K2X 2 +K3X 3

[0026] Among them, F k is the elastic restoring force;

[0027] Nonlinear damping force:

[0028]

[0029] Among them F c is the nonlinear damping force;

[0030] Step 9: Perform third-order polynomial fitting on these hysteresis curves to obtain the values ​​of K1, K2, and K3, and obtain the fitted nonlinear elastic force;

[0031] Step 10: Subtract the fitted nonlinear elastic force from the total restoring force to obtain the nonlinear damping force, and fit the nonlinear damping force to obtain the values ​​of C1 and C2;

[0032] Step 11: Fit the five obtained coefficients with the three parameters of loading amplitude, loading frequency and unit filling rate respectively; under specific working conditions, take the loading amplitude and loading frequency as known conditions, and obtain the hysteresis curve relationship with only the filling rate as a parameter;

[0033] Step 12: Write Matlab code to calculate the damping loss factor corresponding to different filling rates and draw a relationship diagram;

[0034] Step 13: Based on the relationship diagram in step 12, optimize the value of the unit filling rate that maximizes the damping loss factor of the composite unit;

[0035] Step 14: Based on the filling rate determined in step 13, the equivalent material parameters of the composite unit are obtained using step 4, and the damping loss factor of the composite unit is obtained using step 13, which are then filled into the composite vibration damping tool holder to establish a finite element model of the composite vibration damping tool holder.

[0036] Step 15: Based on the finite element model established in step 14, a static analysis simulation is performed to obtain the strain states of the solid tool holder and the composite vibration-damping tool holder with different wall thicknesses, thereby completing the wall thickness design of the tool holder;

[0037] Step 16: Based on the finite element model established in step 14, a simulation harmonic response analysis is performed to obtain the attenuation of the response at the tool tip over time at different filling positions, thereby completing the design of the filling position of the composite unit in the tool handle cavity.

[0038] In one embodiment, the fitting formula of step 11 is as follows:

[0039] K1=a1ρ+a2ρ 2 +a3ρ 3 +a4ρ 4 +a5ρ 5

[0040] K2=b1+b2a+b3ρ+b4p+b5ρ 2 +b6p 2 +b7a 2 +b8ρp+b9ap+b 10 aρ

[0041] +b 11 ρ 3 +b 12 p 3 +b 13 ρ 2 p 2 +b 14 ρp 2 +b 15 aρp+b 16 ρ 4

[0042] K3=c1+c2a+c3ρ+c4p+c5ρ 2 +c6p 2 +c7a 2 +c8ρp+c9ap+c 10 aρ

[0043] +c 11 ρ 3 +c 12 p 3 +c 13 ρ 2 p 2 +c 14 ρp 2 +c 15 aρp+c 16 ρ 4

[0044]

[0045]

[0046] Among them, a1-a5 are the unknown coefficients in the fitting formula of the first-order nonlinear elastic force coefficient, b1-b 16 is the unknown coefficient in the fitting formula of the second-order nonlinear elastic force coefficient, c1-c 16 are the undetermined coefficients in the fitting formula of the third-order nonlinear elastic force coefficient, d1-d6 are the undetermined coefficients in the fitting formula of the linear damping term coefficient, e1-e5 are the undetermined coefficients in the fitting formula of the nonlinear damping term coefficient, a is the loading amplitude, p is the loading frequency, and ρ is the filling rate.

[0047] In one embodiment, the fitting formula in step 11 is substituted into the nonlinear dynamic model of the hysteresis curve in step 9 to obtain:

[0048]

[0049] Where t is time.

[0050] In one embodiment, the material parameters obtained in step 4 include viscoelastic and hyperelastic material parameters of the metal-polymer composite unit.

[0051] The above technical features can be combined in various suitable ways or replaced by equivalent technical features, such as any metal configuration and any polymer material as long as the purpose of the present invention can be achieved.

[0052] The design method of a filler metal-polymer composite vibration-damping toolholder provided by the present invention has at least the following beneficial effects compared with the prior art:

[0053] A composite structure has been introduced to a conventional high-feed milling toolholder, ensuring its operational rigidity while also improving its damping and reducing the forced vibrations that can easily occur during high-feed milling. This invention enables the design of any configuration to maximize damping under specific operating conditions. BRIEF DESCRIPTION OF THE DRAWINGS

[0054] The present invention will be described in more detail below based on embodiments and with reference to the accompanying drawings, wherein:

[0055] Figure 1 Schematic diagram of the composite handle structure of an example of the present invention;

[0056] Figure 2 Schematic diagram of the composite unit structure that can be used in the present invention;

[0057] Figure 3 Schematic diagram of the metal unit structure that can be used in the present invention;

[0058] Figure 4 is a graph showing the relationship between the filling rate of the composite unit structure and the damping loss factor used in the present invention;

[0059] Figure 5 This is the strain cloud diagram of the example tool holder with different wall thickness;

[0060] Figure 6 This is a graph showing the tool tip response versus time for different fill positions on the example tool holder;

[0061] Figure 7 This is a frequency response comparison diagram of a composite tool handle and a solid tool handle in an embodiment of the method of the present invention;

[0062] Figure 8 This is a comparison diagram of acceleration signals of a composite tool holder and a solid tool holder when milling at a cutting depth of 0.5 mm and a feed rate of 384 mm / min in an embodiment of the method of the present invention;

[0063] Figure 9 This is a comparison diagram of acceleration signals of a composite tool holder and a solid tool holder when milling at a cutting depth of 0.8 mm and a feed rate of 384 mm / min in an embodiment of the method of the present invention;

[0064] Figure 10 This is a comparison diagram of acceleration signals of a composite tool holder and a solid tool holder when milling at a cutting depth of 0.3 mm and a feed rate of 512 mm / min in an embodiment of the method of the present invention;

[0065] In the figure, 1-metal unit, 2-polymer material, 3-torque groove, 4-basic tool handle, 5-positioning key, 6-positioning core shaft, 11A-straight beam A, 12A-inclined beam A, 11B-straight beam B, 12B-inclined beam B, 11C-straight beam C, 12C-inclined beam C. DETAILED DESCRIPTION

[0066] The present invention will be further described below with reference to the accompanying drawings.

[0067] Design example: Design of metal-polymer composite vibration damping tool holder. The structure of the vibration damping tool holder is as follows: Figure 1 shown.

[0068] The handle model designed in this example is BT40-FMB22-150, and the material used is 17-4PH stainless steel.

[0069] Step 1: Determine the configuration of the metal unit and the type of polymer material.

[0070] The tool is filled with a metal unit structure. The design of the metal unit size is affected by the additive printing accuracy and is selected to be 5mm. The metal unit sample for the cyclic tensile test is manufactured using additive manufacturing technology. The sample is 110mm long, of which the metal unit part is 60mm long, 25mm wide, and 10mm high.

[0071] Three polymer materials were selected: polyurethane (PU), epoxy resin (EP) and silicone rubber (SR).

[0072] Combining two by two, cyclic tensile tests were carried out on the fatigue testing machine to obtain the hysteresis curves of different combinations and calculate the damping loss factors, as shown in Table 1. By comparing the damping loss factors, BCCZ-EP was selected. The composite unit structure is as follows Figure 2 As shown, the metal unit is Figure 3 shown.

[0073] Table 1

[0074]

[0075] Step 2: A compression test was performed on the epoxy resin material to obtain its Yeoh hyperelastic model fitting parameters, as shown in Table 2. A stress relaxation test was performed on the epoxy resin material to obtain its viscoelastic parameters, as shown in Table 3.

[0076] Step 3: Establish a finite element model of the composite unit, perform compression simulation and stress relaxation simulation on it, and set the interface of the two-phase material as a binding relationship. The material properties of 17-4PH are shown in Table 4.

[0077] Step 4: Input the material parameters obtained in step 2, output the force-displacement curve of the composite unit, and perform data processing on it to obtain the equivalent material parameters of the composite unit.

[0078] Step 5: Establish a finite element model corresponding to the cyclic tensile test, input the material parameters equivalent to the composite unit obtained in step 4, set the sinusoidal displacement excitation, and output the hysteresis curve.

[0079] Table 2

[0080]

[0081] Table 3

[0082]

[0083] Table 4

[0084]

[0085] In step 6, three parameters were designed: loading amplitude, loading frequency, and fill rate. The loading amplitude was set to five levels: 0.1587 mm, 0.1959 mm, 0.2391 mm, 0.2775 mm, and 0.3153 mm; the loading frequency was set to five levels: 0.5 Hz, 1 Hz, 2 Hz, 4 Hz, and 5 Hz; and the fill rate was set to five levels: 0.18, 0.26, 0.34, 0.42, and 0.5. Based on the selected factor levels, 32 sets of hysteresis curves were simulated using the finite element model proposed in steps 2 to 6.

[0086] Step 7: Establish the hysteresis curve nonlinear dynamic model of the composite unit:

[0087]

[0088] Where F is the restoring force, X is the deformation of the composite unit structure, is the velocity of the composite unit structure, K1, K2, and K3 are the first-order nonlinear elastic force coefficient, the second-order elastic force coefficient, and the third-order elastic force coefficient, respectively. C1 is the linear damping term coefficient, and C2 is the nonlinear damping term coefficient.

[0089] Step 8: Decompose the hysteresis curve into nonlinear elastic force and nonlinear damping force.

[0090] Nonlinear elastic force:

[0091] F k (X) = K1X + K2X 2 +K3X 3

[0092] Among them, F k is the elastic restoring force.

[0093] Nonlinear damping force:

[0094]

[0095] Among them F c is the nonlinear damping force.

[0096] Step 9: Perform third-order polynomial fitting on these hysteresis curves to obtain the values ​​of K1, K2, and K3, and thus obtain the fitted nonlinear elastic force.

[0097] Step 10: Subtract the fitted nonlinear elastic force from the total restoring force to obtain the nonlinear damping force, and fit the nonlinear damping force to obtain the values ​​of C1 and C2.

[0098] Step 11: Fit the five coefficients obtained with three parameters: loading amplitude, loading frequency, and filling rate. The fitting formula is as follows.

[0099] K1=a1ρ+a2ρ 2 +a3ρ 3 +a4ρ 4 +a5ρ 5

[0100] K2=b1+b2a+b3ρ+b4p+b5ρ 2 +b6p 2 +b7a 2 +b8ρp+b9ap+b 10 aρ

[0101] +b 11 ρ 3 +b 12 p 3 +b 13 ρ 2 p 2 +b 14 ρp 2 +b 15 aρp+b 16 ρ 4

[0102] K3=c1+c2a+c3ρ+c4p+c5ρ 2 +c6p 2 +c7a 2 +c8ρp+c9ap+c 10 aρ

[0103] +c 11 ρ 3 +c 12 p 3 +c 13 ρ 2 p 2 +c 14 ρp 2 +c 15 aρp+c 16 ρ 4

[0104]

[0105]

[0106] Among them, a1-a5 are the undetermined coefficients in the fitting formula of the first-order nonlinear elastic force coefficient, as shown in Table 5, b1-b 16 is the unknown coefficient in the fitting formula of the second-order nonlinear elastic force coefficient, as shown in Table 6, c1-c 16are the undetermined coefficients in the fitting formula of the third-order nonlinear elastic force coefficient, as shown in Table 7, d1-d6 are the undetermined coefficients in the fitting formula of the linear damping term coefficient, as shown in Table 8, e1-e5 are the undetermined coefficients in the fitting formula of the nonlinear damping term coefficient, as shown in Table 9, a is the loading amplitude, p is the loading frequency, and ρ is the filling rate.

[0107] Table 5

[0108]

[0109] Table 6

[0110]

[0111] Table 7

[0112]

[0113]

[0114] Table 8

[0115]

[0116] Table 9

[0117]

[0118] Step 12: Substitute the fitting formula in step 11 into the nonlinear dynamic model of the hysteresis curve in step 9 to obtain:

[0119]

[0120] Where t is time.

[0121] Step 13: Under specific working conditions, the loading amplitude is 0.15 mm and the loading frequency is 5 Hz. Use step 12 to obtain the hysteresis curve relationship with only the filling rate as a parameter.

[0122] Step 14, write Matlab code to calculate the damping loss factor corresponding to different filling rates and draw a relationship diagram. Figure 2 shown.

[0123] Step 15: Based on the relationship diagram in step 14, the value of the filling rate that maximizes the damping loss factor of the composite unit is optimized, and the filling rate value is 0.237.

[0124] Step 16: Based on the filling rate and the corresponding damping loss factor determined in step 15, the equivalent material parameters of the composite unit are obtained using step 4, and are filled into the composite tool holder to establish a finite element model of the composite tool holder.

[0125] Step 17. Select the appropriate handle wall thickness.

[0126] In the finite element simulation model, when the wall thickness of the tool holder is 1mm and 2mm respectively, a concentrated force of 1000N is applied to the tool tip in the x, y, and z directions, and a fixed constraint is applied to the tool holder for simulation analysis. The strain state of the tool holder is as follows: Figure 5 When the wall thickness is 1 mm, the strain of the composite tool holder is one order of magnitude different from that of the solid tool holder, and the difference in the median strain is 5×10 -4 When the wall thickness is 2mm, the strain of the composite tool handle is not much different from that of the solid tool handle, so the tool handle wall thickness of 2mm is selected.

[0127] Step 18: Select the appropriate composite unit filling position.

[0128] In the finite element simulation model, the composite unit filling positions are near the tool tip and near the clamping area. A concentrated force of 1000N is applied to the tool tip in the x, y, and z directions. A fixed constraint is applied to the tool shank for simulation analysis. The response changes at the tool tip at different positions are as follows: Figure 6 As shown in the figure, when the composite unit filling position is closer to the tool tip, its damping effect is more obvious, the vibration decays faster, and the amplitude is lower. Therefore, the composite unit is selected to be filled near the tool tip.

[0129] In summary, the final configuration selected for this example is a BCCZ unit structure with a filling ratio of 0.237. The metal-polymer composite vibration damping tool holder uses epoxy resin to fill the metal pores. After modal knocking experiments, the first-order modal damping ratios of the composite tool holder and the solid tool holder are 0.183% and 0.0865%, respectively. Compared with the solid tool holder, the first-order modal damping ratio of the composite tool holder is improved by 111.56%. The tool holder frequency response function is compared. Figure 7 shown.

[0130] Figure 8 、 Figure 9 、 Figure 10 The acceleration signals of the tool holder in this embodiment and the traditional solid tool holder under different milling parameters are shown. It can be seen that the tool designed in the embodiment is relatively stable during the milling process with different parameters, but the amplitude of the traditional solid tool holder fluctuates more violently during the milling process, and the fluctuation becomes more violent as the cutting depth increases.

[0131] Table 10 calculates the RMS values ​​of different signals. The composite toolholder exhibits excellent vibration reduction under most cutting parameters. Table 11 shows the peak values ​​of the cutting force and acceleration signals obtained by removing eccentricity and averaging them. The vibration-damping toolholder reduced the average peak acceleration in the x-direction by 22.97%, the average peak acceleration in the y-direction by 16.1%, the average peak acceleration in the z-direction by 15.26%, and the average combined peak acceleration by 24.66%. The average peak cutting force in the x-direction, the average peak cutting force in the y-direction, and the average peak cutting force in the z-direction decreased by 19.05%, 19.4%, and 14.06%, respectively, for a total combined peak cutting force of 15.74%.

[0132] Table 10

[0133]

[0134]

[0135] Table 11

[0136]

[0137]

[0138] Although the present invention is described herein with reference to specific embodiments, it should be understood that these embodiments are merely illustrative of the principles and applications of the invention. It should be understood that many modifications may be made to the illustrative embodiments, and that other arrangements may be devised, without departing from the spirit and scope of the invention as defined by the appended claims. It should be understood that the various dependent claims and features described herein may be combined in ways other than those described in the original claims. It should also be understood that features described in conjunction with individual embodiments may be employed in conjunction with other described embodiments.

Claims

1. A composite vibration-damping tool handle filled with metal-polymer material, characterized in that: It includes metal structure, polymer material, torque groove and basic tool handle; the polymer material fills the pores of the metal structure to form a metal-polymer composite structure; The torque groove is located between the metal-polymer composite structure and the basic tool handle.

2. The composite vibration-damping tool handle made of filler metal and polymer material according to claim 1, characterized in that: The metal structure includes a plurality of metal units, and each metal unit includes a plurality of inclined beams with common end points and a plurality of straight beams for connecting the other ends of the inclined beams.

3. The composite vibration-damping tool handle made of filler metal and polymer material according to claim 2, characterized in that: The common endpoint is replaced by a regular hexahedron structure composed of a plurality of metal beams.

4. The composite vibration-damping tool handle made of filler metal and polymer material according to claim 1, characterized in that: The metal structure includes a plurality of metal units, each of which includes a plurality of straight beams parallel to each other, and adjacent straight beams are connected by crossed oblique beams.

5. The composite vibration-damping tool handle made of filler metal and polymer material according to claim 1, characterized in that: The metal material is stainless steel.

6. The composite vibration-damping tool handle made of filler metal and polymer material according to claim 1, characterized in that: The polymer material is polyurethane, epoxy resin or silicone rubber.

7. A design method for a composite vibration-damping tool handle filled with metal-polymer material, characterized in that: include: Step 1: Perform cyclic tensile tests on samples of different configurations and different polymer material combinations to obtain their hysteresis curves and calculate their respective damping loss factors, and select the configuration and polymer material combination with the highest damping loss factor; Step 2: Perform uniaxial compression and stress relaxation tests on the polymer material to obtain its hyperelastic and viscoelastic material parameters; Step 3: Establish a finite element model of the metal-polymer composite unit and perform compression simulation and stress relaxation simulation on it; Step 4: Input the material parameters obtained in step 2, obtain its force-displacement curve, and obtain the linear elastic and viscoelastic material parameters of the composite element; Step 5: Establish a finite element model corresponding to the cyclic tensile test, input the material parameters obtained in step 4, set the sinusoidal displacement control, and output the corresponding hysteresis curve; Step 6: Based on the combination of the configuration with the maximum damping loss factor obtained in step 1 and the polymer material, the finite element process of steps 2 to 6 is used to obtain multiple sets of different hysteresis curves; Step 7: Establish the hysteresis curve nonlinear dynamic model of the composite unit: Where F is the restoring force, X is the deformation of the composite element, is the deformation velocity of the composite unit, K1, K2, and K3 are the first-order nonlinear elastic force coefficient, the second-order elastic force coefficient, and the third-order elastic force coefficient, respectively; C1 is the linear damping term coefficient, and C2 is the nonlinear damping term coefficient; Step 8: Decompose the hysteresis curve into nonlinear elastic force and nonlinear damping force; Nonlinear elastic force: F k (X)=K1X+K2X 2 +K3X 3 Among them, F k is the elastic restoring force; Nonlinear damping force: Among them F c is the nonlinear damping force; Step 9: Perform third-order polynomial fitting on these hysteresis curves to obtain the values ​​of K1, K2, and K3, and obtain the fitted nonlinear elastic force; Step 10: Subtract the fitted nonlinear elastic force from the total restoring force to obtain the nonlinear damping force, and fit the nonlinear damping force to obtain the values ​​of C1 and C2; Step 11: Fit the five obtained coefficients with the three parameters of loading amplitude, loading frequency and unit filling rate respectively; under specific working conditions, take the loading amplitude and loading frequency as known conditions, and obtain the hysteresis curve relationship with only the filling rate as a parameter; Step 12: Calculate the damping loss factors corresponding to different filling rates and draw a relationship diagram; Step 13: Based on the relationship diagram in step 12, optimize the value of the unit filling rate that maximizes the damping loss factor of the composite unit; Step 14: Based on the filling rate determined in step 13, the equivalent material parameters of the composite unit are obtained using step 4, and the damping loss factor of the composite unit is obtained using step 13, which are then filled into the composite vibration damping tool holder to establish a finite element model of the composite vibration damping tool holder. Step 15: Based on the finite element model established in step 14, a static analysis simulation is performed to obtain the strain states of the solid tool holder and the composite vibration-damping tool holder with different wall thicknesses, thereby completing the wall thickness design of the tool holder; Step 16: Based on the finite element model established in step 14, a simulation harmonic response analysis is performed to obtain the attenuation of the response at the tool tip over time at different filling positions, thereby completing the design of the filling position of the composite unit in the tool handle cavity.

8. The design method of a composite vibration-damping tool handle made of a filler metal-polymer material according to claim 1, characterized in that: The fitting formula for step 11 is as follows: K1=a1ρ+a2ρ 2 +a3p 3 +a4p 4 +a5r 5 <h2 style=";text-align:left;direction:ltr">K2=b1+b2a+b3ρ+b4p+b5ρ<h2 style=";text-align:left;direction:ltr"> 2 <h2 style=";text-align:left;direction:ltr"> +b6p<h2 style=";text-align:left;direction:ltr"> 2 <h2 style=";text-align:left;direction:ltr"> +b7a<h2 style=";text-align:left;direction:ltr"> 2 <h2 style=";text-align:left;direction:ltr"> +b8ρp+b9ap+b<h2 style=";text-align:left;direction:ltr"> 10 <h2 style=";text-align:left;direction:ltr"> aρ +b 11 r 3 +b 12 p 3 +b 13 r 2 p 2 +b 14 p p 2 +b 15 arp+b 16 r 4 K3=c1+c2a+c3ρ+c4p+c5ρ 2 +c6p 2 +c7a 2 +c8ρp+c9ap+c 10 aρ +c 11 r 3 +c 12 p 3 +c 13 r 2 p 2 +c 14 p p 2 +c 15 arp+c 16 r 4 Among them, a1-a5 are the unknown coefficients in the fitting formula of the first-order nonlinear elastic force coefficient, b1-b 16 is the unknown coefficient in the fitting formula of the second-order nonlinear elastic force coefficient, c1-c 16 are the undetermined coefficients in the fitting formula of the third-order nonlinear elastic force coefficient, d1-d6 are the undetermined coefficients in the fitting formula of the linear damping term coefficient, e1-e5 are the undetermined coefficients in the fitting formula of the nonlinear damping term coefficient, a is the loading amplitude, p is the loading frequency, and ρ is the filling rate.

9. The design method of a composite vibration-damping tool handle made of a filler metal-polymer material according to claim 1, characterized in that: Substituting the fitting formula in step 11 into the nonlinear dynamic model of the hysteresis curve in step 9 yields: Where t is time.

10. The design method of a composite vibration-damping tool handle made of a filler metal-polymer material according to claim 1, characterized in that: The material parameters obtained in step 4 include the viscoelastic and hyperelastic material parameters of the metal-polymer composite unit.

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