CN114036671A - Cutting force model modeling method considering spindle thermal error and cutter bounce - Google Patents
Cutting force model modeling method considering spindle thermal error and cutter bounce Download PDFInfo
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Abstract
The invention discloses a cutting force model modeling method considering spindle thermal error and cutter bounce, which comprises the following steps: 1) establishing a cutting force theoretical model under ideal conditions; 2) considering the cutter runout, solving the cutter shaft offset distance rho and the cutter shaft offset angle phi caused by the cutter runoutro(ii) a 3) The thermal error of the main shaft is considered, and the offset distance rho and the offset angle phi of the cutter shaft are corrected by the thermal error of the main shaft in a thermal balance stateroObtaining the corrected offset distance rho of the cutter shaft1Offset angle phi from cutter shaftr1By the offset distance rho of the cutter shaft1Offset angle phi from cutter shaftr1And correcting the cutting force theoretical model to obtain a cutting force model considering cutter bounce and thermal errors. The invention relates to a cutting force model considering the thermal error of a main shaft and the jumping of a cutter and a modeling method thereof,the influence of the thermal error of the main shaft and the cutter bounce on the cutting force is considered, so that the actual machining condition can be better met.
Description
Technical Field
The invention belongs to the technical field of machining, and particularly relates to a cutting force model modeling method considering spindle thermal error and cutter bounce.
Background
Existing cutting force studies are generally predicted under ideal conditions, namely: the shape of the tool is strictly centrosymmetric and rotates around its axis, and the material removal process does not have any effect on the tool shape. For example, the cutting force modeling method of the fine PCD milling cutter without the side edge relief angle disclosed in the chinese patent application with the publication number CN 113536543 a and the modeling method of the static milling force of the ball end mill based on the semi-analytical method disclosed in the chinese patent application with the publication number CN 113297696 a are all implemented under the ideal conditions of cutting, however, in actual machining, the cutter may jump, the spindle may also generate a thermal error after long-time operation, and both the cutter jump and the spindle thermal error may cause the cutter shaft to be cheap, thereby causing the cutting force to change.
Disclosure of Invention
In view of the above, the present invention provides a cutting force model modeling method considering spindle thermal error and tool run-out, which can better meet the actual machining conditions by considering the influence of the spindle thermal error and the tool run-out on the cutting force.
In order to achieve the purpose, the invention provides the following technical scheme:
a cutting force model modeling method considering spindle thermal error and cutter bounce comprises the following steps:
1) establishing a cutting force theoretical model under ideal conditions;
2) considering the cutter runout, solving the cutter shaft offset distance rho and the cutter shaft offset angle phi caused by the cutter runoutro;
3) The thermal error of the main shaft is considered, and the offset distance rho and the offset angle phi of the cutter shaft are corrected by the thermal error of the main shaft in a thermal balance stateroObtaining the corrected offset distance rho of the cutter shaft1Offset angle with cutter shaftφr1By the offset distance rho of the cutter shaft1Offset angle phi from cutter shaftr1And correcting the cutting force theoretical model to obtain a cutting force model considering cutter bounce and thermal errors.
Further, in the step 1), the modeling method of the cutting force theoretical model under the ideal condition is as follows:
dividing the cutter into M layers of infinitesimal cutting edges along the cutter shaft, decomposing the cutting force generated by any infinitesimal cutting edge into tangential cutting force, radial cutting force and axial cutting force, and then the cutting force model of the infinitesimal cutting edge is as follows:
wherein, Kte,Kre,KaeExpressing the tangential, radial and secondary normal ploughing power cutting coefficients of the infinitesimal cutting edge, Ktc,Krc,KacRespectively representing the tangential, radial and secondary normal shearing force cutting coefficients of the infinitesimal cutting edge; dS and db respectively represent the length and width of the infinitesimal cutting edge; uct0(φ, κ) represents the undeformed chip thickness, related to the infinitesimal point position angle ψ and infinitesimal point axial immersion angle κ of the infinitesimal cutting edge, and:
ψ=θ+(i-1)φp-φz
wherein θ represents a cutting edge position angle measured at the tip; phi is azThe helical retardation angle, phi, of a cutting edge infinitesimal with respect to the position of the tipz=ztan(i0)/R,i0Representing a helix angle; phi is apIndicates the tool tip angle of the toolp2 pi/N, wherein N is the number of cutter teeth; i denotes the i-th cutting edge;
uct0(ψ,κ)=n·f
n=(sin(κ)sin(ψ),sin(κ)cos(ψ),cos(κ))T
wherein i0Representing a helix angle; n represents the normal at the surface of the infinitesimal cutting edge; dz represents the infinitesimal cutting edge thickness; f is a feed vector;
converting the cutting force model of the infinitesimal cutting edge into a tool coordinate system to obtain:
wherein dFx、dFyAnd dFzRespectively representing the components of the cutting force of the infinitesimal cutting edge in the directions of X, Y and Z axis;
and (3) integrating and accumulating the cutting force of the infinitesimal cutting edge to obtain the cutting force of the cutter, namely a cutting force theoretical model:
wherein, Fx、FyAnd FzRepresenting the components of the tool cutting force in the X, Y and Z-axis directions, respectively.
Further, the cutter shaft offset distance ρ and the cutter shaft offset angle φ caused by the cutter shaft runoutroThe solving method comprises the following steps:
at a given position angle τ, the cutting force for one rotation of the tool is:
F(τ)=F0(τ)+ρA1(τ)cos(φro)+ρA2(τ)sin(φro)
wherein, F0(τ) is the theoretical cutting force when the tool is free of runout; k is a radical ofijThe cutting edge position angle of a layer j of infinitesimal cutting edge of the No. i cutting edge is represented; psiijThe axial immersion angle of a layer-j infinitesimal cutting edge of a No. i cutting edge is shown;
the difference in cutting force Δ F at positions between phase angles 2 π/N is:
ΔF=F(τ)-F(τ-φp)=ρ(a1(τ)cos(φro)+a2(τ)sin(φro))
a1=A1(τ)-A1(τ-φp)
a2=A2(τ)-A2(τ-φp)
then:
during one rotation of the tool, a series of tan (phi) values is obtainedro) Using least square fitting method to obtain offset angle phiro(ii) a Will phiroSubstituting the calculation formula of the cutting force difference delta F to obtain a group of data of the cutter shaft offset distance rho, and obtaining the cutter shaft offset distance rho by adopting a minimum quadratic fitting method.
Further, the cutter shaft offset distance ρ is obtained after the spindle generates a thermal error1Offset angle phi from cutter shaftr1Is about deltay,ρ,φr0And:
wherein, deltayIs the thermal drift of the principal axis in the Y direction;
the extra feed f of the tool is caused by both tool runout and spindle thermal errorr1Comprises the following steps:
fr1=(ρ1sin(φr1+θ)-ρ1sin(φr1+θ-φp),ρ1cos(φr1+θ)-ρ1cos(φr1+θ-φp),0)T
additional micro-deformed chip thickness uct corrected by tool runout and spindle thermal errorr1Comprises the following steps:
uctr1=ρ1sin(κ)cos(φr1+φz-(i-1)φp)-ρ1sin(κ)cos(φr1+φz-(i-2)φp)
the cutting force model of the infinitesimal cutting edge considering the tool runout and the spindle thermal error is
And substituting the cutting force model of the infinitesimal cutting edge considering the tool run-out and the spindle thermal error into the cutting force theoretical model to obtain the cutting force model considering the tool run-out and the spindle thermal error.
The invention has the beneficial effects that:
according to the cutting force model modeling method considering the spindle thermal error and the cutter bounce, the theoretical model of the cutting force is corrected by researching the influence of the cutter bounce and the spindle thermal error on the cutter shaft offset distance and the cutter shaft offset angle respectively and jointly considering the cutter bounce and the cutter shaft offset distance and the cutter shaft offset angle after the spindle thermal error, so that the cutting force model considering the cutter bounce and the thermal error can be obtained, and the actual processing conditions can be better met.
Drawings
In order to make the object, technical scheme and beneficial effect of the invention more clear, the invention provides the following drawings for explanation:
FIG. 1 is a flow chart of an embodiment of a cutting force model modeling method of the present invention that takes into account spindle thermal error and tool run-out;
FIG. 2 is a schematic diagram of a tool coordinate system;
FIG. 3 is a schematic structural view of a cutting edge contact segment of the ball end mill;
FIG. 4(a) is a schematic structural diagram of the layered discretization of the cutter;
FIG. 4(b) is a schematic diagram illustrating the calculation of the undeformed cut thickness;
FIG. 5 is a schematic view of undeformed cutting thickness taking into account tool run-out; (a) is a front view; (b) is a top view; (c) the influence of tool jumping on the undeformed cutting thickness;
FIG. 6 is a schematic view of a spindle thermal error detection apparatus;
FIG. 7 is a schematic diagram of spindle offset due to thermal error;
FIG. 8(a) is a schematic view of arbor offset taking into account tool run-out and spindle thermal error;
FIG. 8(b) is a schematic view of the effect of tool run-out and spindle thermal error on undeformed cut thickness;
Detailed Description
The present invention is further described with reference to the following drawings and specific examples so that those skilled in the art can better understand the present invention and can practice the present invention, but the examples are not intended to limit the present invention.
Fig. 1 is a flow chart of an embodiment of a cutting force modeling method of the present invention that takes into account spindle thermal error and tool run-out. The cutting force model modeling method considering the spindle thermal error and the cutter bounce comprises the following steps:
1) establishing a theoretical model of cutting force under ideal conditions
The milling force model is usually established based on a tool coordinate system, and as shown in fig. 2, the tool coordinate system setting method of the present embodiment is as follows:
origin of coordinates: setting the position of the tool nose point as the origin of coordinates of a tool coordinate system;
XTshaft: setting the projection direction of the tool feeding direction in the horizontal plane as the X of the tool coordinate systemTIn the positive direction of the axis, since the present embodiment deals with milling forces in high machining, the feed direction of the tool has been limited to that in the positive directionIn a horizontal plane perpendicular to the axis of the tool, i.e. the feed direction and X of the toolTThe axial directions are parallel;
ZTshaft: setting the direction upward along the tool axis to ZTThe positive direction of the axis;
YTshaft: perpendicular to XT,ZTAnd (4) a plane.
Specifically, in order to predict the cutting force, the tool is divided into M layers of infinitesimal cutting edges along the tool axis, the cutting force generated by any infinitesimal cutting edge is decomposed into a tangential cutting force, a radial cutting force and an axial cutting force, and then the cutting force model of the infinitesimal cutting edge is:
wherein, Kte,Kre,KaeExpressing the tangential, radial and secondary normal ploughing power cutting coefficients of the infinitesimal cutting edge, Ktc,Krc,KacRespectively representing the tangential, radial and secondary normal shearing force cutting coefficients of the infinitesimal cutting edge; dS and db respectively represent the length and width of the infinitesimal cutting edge; uct0(φ, κ) represents the undeformed chip thickness, which is related to the infinitesimal point position angle ψ of the infinitesimal cutting edge and the infinitesimal point axial dip angle κ.
A typical constant lead spherical helix is shown in figure 3. The infinitesimal point position angle psi of the infinitesimal cutting edge is:
ψ=θ+(i-1)φp-φz
wherein θ represents a cutting edge position angle measured at the tip; phi is azThe helical retardation angle, phi, of a cutting edge infinitesimal with respect to the position of the tipz=ztan(i0)/R,i0Representing a helix angle; phi is apIndicates the tool tip angle of the toolp2 pi/N, wherein N is the number of cutter teeth; i represents … …;
as shown in fig. 4(b), the undeformed cut thickness can be expressed as:
uct0(ψ,κ)=n·f
n=(sin(κ)sin(ψ),sin(κ)cos(ψ),cos(κ))T
the length of the infinitesimal cutting edge is:
the width of the infinitesimal cutting edge is:
wherein, i0Representing a helix angle; n represents the normal at the surface of the infinitesimal cutting edge; dz represents the infinitesimal cutting edge thickness; f is a feed vector; f is along XTA directional feed vector.
Converting the cutting force model of the infinitesimal cutting edge into a tool coordinate system to obtain:
wherein dFx、dFyAnd dFzRepresenting the components of the cutting force of the infinitesimal cutting edge in the X, Y and Z-axis directions, respectively.
And (3) integrating and accumulating the cutting force of the infinitesimal cutting edge to obtain the cutting force of the cutter, namely a cutting force theoretical model:
wherein, Fx、FyAnd FzRepresenting the components of the tool cutting force in the X, Y and Z-axis directions, respectively.
2) Considering the cutter runout, solving the cutter shaft offset distance rho and the cutter shaft offset angle phi caused by the cutter runoutro
As shown in fig. 5, the tool runout can be regarded as the tool axis is offset by a distance ρ and an angle Φro. When considering tool runout, the actual feed will include for each revolution of the toolTwo parts, because of the run-out from the geometric center O by the rotation axis0To the actual centre of rotation O1The offset induced feed and the original design feed per tooth. Thus, the effect of tool runout can be considered as an additional feed.
fr=(ρsin(φro+θ)-ρsin(φro+θ-φp),ρcos(φro+θ)-ρcos(φro+θ-φp),0)T
the feed direction is perpendicular to the tool axis. Then, the corresponding additional undeformed cut thickness is obtained, namely:
uctro=ρsin(κ)cos(φro+φz-(i-1)φp)-ρsin(κ)cos(φro+φz-(i-2)φp)
in the presence of tool runout, the cutting forces generated by the current tooth and the previous tooth will be different depending on the runout parameters ρ and φro. By analyzing the cutting signal with the phase difference of 2 pi/N (the sharp angle of the cutter) in the machining of the three-axis machine tool, the offset distance rho and the angle phi generated by the cutter jumping can be obtainedro。
Specifically, the cutter shaft offset distance ρ and the cutter shaft offset angle φ caused by cutter shaft runoutroThe solving method comprises the following steps:
the cutting force in any direction can be used to calculate the run-out parameter. Here, the edge X is usedTDirectional cutting forces are examples. At a given position angle τ, the cutting force for one rotation of the tool is:
uct will be mixedroAfter substitution, we obtain:
F(τ)=F0(τ)+ρA1(τ)cos(φro)+ρA2(τ)sin(φro)
wherein, F0(τ) is the theoretical cutting force when the tool is free of runout; kappaijThe cutting edge position angle of a layer j of infinitesimal cutting edge of the No. i cutting edge is represented; psiijThe axial immersion angle of a layer-j infinitesimal cutting edge of a No. i cutting edge is shown;
the difference in cutting force Δ F at positions between phase angles 2 π/N is:
ΔF=F(τ)-F(τ-φp)=ρ(a1(τ)cos(φro)+a2(τ)sin(φro))
a1=A1(τ)-A1(τ-φp)
a2=A2(τ)-A2(τ-φp)
then in the experimental data, as long as sufficiently large sample data is collected, various values of af can be collected. In each such set of data, one can obtain:
using the measured cutting force data, a series of tan (φ) values can be obtained during one revolution of the toolro) The deviation angle phi is obtained by adopting a least square fitting methodro(ii) a Will phiroSubstituting the calculation formula of the cutting force difference delta F to obtain a group of data of the cutter shaft offset distance rho, and obtaining the cutter shaft offset distance rho by adopting a least square fitting method.
3) The thermal error of the main shaft is considered, and the offset distance rho and the offset angle phi of the cutter shaft are corrected by the thermal error of the main shaft in a thermal balance stateroObtaining the corrected offset distance of the cutter shaftDistance rho1Offset angle phi from cutter shaftr1By the offset distance rho of the cutter shaft1Offset angle phi from cutter shaftr1And correcting the cutting force theoretical model to obtain a cutting force model considering cutter bounce and thermal errors.
In the machining process of the machine tool, under the condition of uneven heat distribution, the machine tool parts are subjected to uneven thermal deformation. In the vertical machining center spindle, the spindle deflects and drifts in the direction X, Y due to the deformation of other parts such as the spindle case.
In order to better detect the thermal effect of a spindle of a numerical control machine tool, according to ISO 230-3 international standards, equipment such as a displacement sensor is utilized, thermal effect deformation is determined according to actual requirements of comprehensive performance test and evaluation of spindle products of a five-axis milling machine, spindle deformation caused by temperature rise caused by spindle rotation is mainly detected, detected data is sorted, and a spindle deformation image caused by the thermal effect is obtained. In the embodiment, a spindle thermal error measuring system shown in FIG. 6 is constructed according to a five-point detection method in the ISO 230-3 standard. Studies have shown that the main effect on spindle distortion is distributed around the spindle head, so when thermally modeling the spindle, the temperature of the spindle head is mainly measured, and the temperature sensor mounting positions are shown in table 1.
TABLE 1 temperature sensor mounting location
Placing position | Function of | |
T1~T3 | Main spindle box (Upper, lower, side) | Measuring spindle heating |
T4~T5 | Main shaft sleeve | Measuring spindle heating |
T6 | Spindle motor | Measuring heating of an electric machine |
T7 | Machine tool shell | Measuring ambient temperature |
As shown in FIG. 6, X1,X2The thermal drift of the main shaft mean line in the X direction is approximately replaced by the error measured by the displacement sensor in the X direction; y is1,Y2The thermal drift of the main shaft mean line in the Y direction is approximately replaced by the error measured by the displacement sensor in the Y direction; z is a thermal error measured by a Z-direction sensor and is a main shaft Z thermal elongation obtained by direct measurement;
as shown in FIG. 7, line A assumes that the check rod does not deform during operation of the machine tool0B0Checking the position of the stick for initial value, A1B1Spindle inspection stick position after thermal error for the spindle occurs. A. thex,BxSpindle inspection stick position A after thermal error1B1Projection in the X direction, for the same reason Ay,ByIs A1B1Projected in the Y direction. Through the analysis of the geometric relationship, an accurate expression of the five-term error can be obtained. In the formula ofx,δyRespectively X, Y direction thermal drift. Alpha is alphax,αyThermal tilts, delta, about axis Y, X, respectivelyzIs Z-direction thermal elongation, X1,X2Is the variation value of the displacement sensor in the X direction. Y is1,Y2The variation value of the displacement sensor in the Y direction and the axial displacement of the main shaft in the Z directionThe change value of the sensor. Hx,HyDistance between two sensors in direction X, Y, Lx,LyX, Y distance of the direction end sensor from the end face of the spindle. In the trapezium formed in the figure, it is easy to ignore high order small quantities according to a simple geometrical relationship:
the thermal error of the main shaft can cause the thermal inclination of the main shaft, but the inclination angle alpha is very small, the influence on error compensation can be ignored, and the compensation value is irrelevant to the length of a cutter when the thermal error is compensated. In addition, the radial offset in the X direction is negligible, and because the present embodiment mainly considers the influence of the offset of the spindle in the X-Y plane and the tool runout on the spindle offset, thereby causing the change of the cutting force, the extension of the spindle in the Z direction caused by the thermal error is not considered temporarily. In summary, in the embodiment, when considering the influence of the thermal error on the cutting force, only the Y thermal drift δ needs to be consideredyThe value of (2) is sufficient.
According to the measured thermal error deltayThe thermal error model can be established with the temperature T of the machine tool:
δy=(T,V)
in the formula, T represents the measured temperature, and V represents the rotation speed of the spindle.
Specifically, the cutter shaft offset distance ρ caused by cutter shaft runout and spindle thermal error1Cutter shaftOffset angle phir1The solving method comprises the following steps:
the thermal error is considered again on the basis of the tool runout, and the tool offset is shown in fig. 8(a) and 8 (b). After thermal errors are considered, the cutter shaft is offset by a distance rho and an angle phiroWill become the offset distance ρ1Angle phi ofr1. From the geometric relationship, ρ1,φr1Is about deltay,ρ,φr0And:
wherein, deltayIs the thermal drift of the principal axis in the Y direction.
The extra feed f of the tool is caused by both tool runout and spindle thermal errorr1Comprises the following steps:
fr1=(ρ1sin(φr1+θ)-ρ1sin(φr1+θ-φp),ρ1cos(φr1+θ)-ρ1cos(φr1+θ-φp),0)T
additional micro-deformed chip thickness uct corrected by tool runout and spindle thermal errorr1Comprises the following steps:
uctr1=ρ1sin(κ)cos(φr1+φz-(i-1)φp)-ρ1sin(κ)cos(φr1+φz-(i-2)φp)
wherein theta is a cutting edge position angle measured at the tool nose; phi is azHelical lag angle phi of cutting edge infinitesimal element relative to tool tip positionz=ztan(i0)/R,i0Is the helix angle; phi is apIs the sharp angle of the cutterp2 pi/N, and N is the number of teeth.
The cutting force model of the infinitesimal cutting edge considering the tool runout and the spindle thermal error is
And substituting the cutting force model of the infinitesimal cutting edge considering the tool run-out and the spindle thermal error into the cutting force theoretical model to obtain the cutting force model considering the tool run-out and the spindle thermal error.
In the cutting force model modeling method considering the spindle thermal error and the cutter runout, the theoretical cutting force model is corrected by researching the influence of the cutter runout and the spindle thermal error on the cutter shaft offset distance and the cutter shaft offset angle respectively and jointly considering the cutter shaft offset distance and the cutter shaft offset angle after the cutter runout and the spindle thermal error, so that the cutting force model considering the cutter runout and the thermal error can be obtained, and the actual processing conditions can be better met.
The above-mentioned embodiments are merely preferred embodiments for fully illustrating the present invention, and the scope of the present invention is not limited thereto. The equivalent substitution or the change made by the person skilled in the art on the basis of the present invention are within the protection scope of the present invention. The protection scope of the invention is subject to the claims.
Claims (4)
1. A cutting force model modeling method considering spindle thermal error and cutter bounce is characterized in that: the method comprises the following steps:
1) establishing a cutting force theoretical model under ideal conditions;
2) considering the cutter runout, solving the cutter shaft offset distance rho and the cutter shaft offset angle phi caused by the cutter runoutro;
3) The thermal error of the main shaft is considered, and the offset distance rho and the offset angle phi of the cutter shaft are corrected by the thermal error of the main shaft in a thermal balance stateroObtaining the corrected offset distance rho of the cutter shaft1Offset angle phi from cutter shaftr1By the offset distance rho of the cutter shaft1Offset angle phi from cutter shaftr1And correcting the cutting force theoretical model to obtain a cutting force model considering cutter bounce and thermal errors.
2. The cutting force model modeling method taking into account spindle thermal error and tool run-out according to claim 1, characterized in that: in the step 1), the modeling method of the cutting force theoretical model under the ideal condition comprises the following steps:
dividing the cutter into M layers of infinitesimal cutting edges along the cutter shaft, decomposing the cutting force generated by any infinitesimal cutting edge into tangential cutting force, radial cutting force and axial cutting force, and then the cutting force model of the infinitesimal cutting edge is as follows:
wherein, Kte,Kre,KaeExpressing the tangential, radial and secondary normal ploughing power cutting coefficients of the infinitesimal cutting edge, Ktc,Krc,KacRespectively representing the tangential, radial and secondary normal shearing force cutting coefficients of the infinitesimal cutting edge; dS and db respectively represent the length and width of the infinitesimal cutting edge; uct0(φ, κ) represents the undeformed chip thickness, related to the infinitesimal point position angle ψ and infinitesimal point axial immersion angle κ of the infinitesimal cutting edge, and:
ψ=θ+(i-1)φp-φz
wherein θ represents a cutting edge position angle measured at the tip; phi is azThe helical lag angle, phi, of a cutting edge infinitesimal element relative to the position of the tipz=ztan(i0)/R,i0Representing a helix angle; phi is apIndicates the tool tip angle of the toolp2 pi/N, wherein N is the number of cutter teeth; i denotes the i-th cutting edge;
uct0(ψ,κ)=n·f
n=(sin(κ)sin(ψ),sin(κ)cos(ψ),cos(κ))T
wherein i0Representing a helix angle; n represents the normal at the surface of the infinitesimal cutting edge; dz represents the infinitesimal cutting edge thickness; f is a feed vector;
converting the cutting force model of the infinitesimal cutting edge into a tool coordinate system to obtain:
wherein dFx、dFyAnd dFzRespectively representing the components of the cutting force of the infinitesimal cutting edge in the directions of X, Y and Z axis;
and (3) integrating and accumulating the cutting force of the infinitesimal cutting edge to obtain the cutting force of the cutter, namely a cutting force theoretical model:
wherein, Fx、FyAnd FzRepresenting the components of the tool cutting force in the X, Y and Z-axis directions, respectively.
3. The cutting force model modeling method taking into account spindle thermal error and tool run-out according to claim 2, characterized in that: cutter shaft offset distance rho and cutter shaft offset angle phi caused by cutter shaft jumpingroThe solving method comprises the following steps:
at a given position angle τ, the cutting force for one rotation of the tool is:
F(τ)=F0(τ)+ρA1(τ)cos(φro)+ρA2(τ)sin(φro)
wherein, F0(τ) is the theoretical cutting force when the tool is free of runout; kappaijThe position angle of a layer of infinitesimal cutting edge of a No. i cutting edge j is shown; psiijThe axial immersion angle of a layer-j infinitesimal cutting edge of a No. i cutting edge is shown;
the difference in cutting force Δ F at positions between phase angles 2 π/N is:
ΔF=F(τ)-F(τ-φp)=ρ(a1(τ)cos(φro)+a2(τ)sin(φro))
a1=A1(τ)-A1(τ-φp)
a2=A2(τ)-A2(τ-φp)
then:
during one rotation of the tool, a series of tan (phi) values is obtainedro) Using least square fitting method to obtain offset angle phiro(ii) a Will phiroSubstituting the calculation formula of the cutting force difference delta F to obtain a group of data of the cutter shaft offset distance rho, and obtaining the cutter shaft offset distance rho by adopting a least square fitting method.
4. The cutting force model modeling method taking into account spindle thermal error and tool run-out as claimed in claim 3, wherein: cutter shaft offset distance rho after main shaft generates thermal error1Offset angle phi from cutter shaftr1Is about deltay,ρ,φr0And:
wherein, deltayIs the thermal drift of the principal axis in the Y direction;
the extra feed f of the tool is caused by both tool runout and spindle thermal errorr1Comprises the following steps:
fr1=(ρ1sin(φr1+θ)-ρ1sin(φr1+θ-φp),ρ1cos(φr1+θ)-ρ1cos(φr1+θ-φp),0)T
additional micro-deformed chip thickness uct corrected by tool runout and spindle thermal errorr1Comprises the following steps:
uctr1=ρ1sin(κ)cos(φr1+φz-(i-1)φp)-ρ1sin(κ)cos(φr1+φz-(i-2)φp)
the cutting force model of the infinitesimal cutting edge considering the tool runout and the spindle thermal error is
And substituting the cutting force model of the infinitesimal cutting edge considering the cutter bounce and the main shaft thermal error into the cutting force theoretical model to obtain the cutting force model considering the cutter bounce and the thermal error.
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