# Dynamics Analysis of Unbalanced Motorized Spindles Supported on Ball Bearings

Authors: Junfeng Liu; Tao Lai; Xiaoan Chen
Journal: Shock and Vibration
 (2016)

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## Abstract

This paper presents an improved dynamic model for unbalanced high speed motorized spindles. The proposed model includes a Hertz contact force model which takes into the internal clearance and an unbalanced electromagnetic force model based on the energy of the air magnetic field. The nonlinear characteristic of the model is analysed by Lyapunov stability theory and numerical analysis to study the dynamic properties of the spindle system. Finally, a dynamic operating test is carried out on a DX100A-24000/20-type motorized spindle. The good agreement between the numerical solutions and the experimental data indicates that the proposed model is capable of accurately predicting the dynamic properties of motorized spindles. The influence of the unbalanced magnetic force on the system is studied, and the sensitivities of the system parameters to the critical speed of the system are obtained. These conclusions are useful for the dynamic design of high speed motorized spindles.


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## Body

## 1. Introduction

Due to the complexity of the reliability and performance problems caused by profound high speed effects [1–3], the machine tools capable of achieving the high speed cutting were first introduced commercially in 1980s, which lags behind the theory of high speed metal cutting by 50 years [4]. Motorized spindles are the core components of CNC machine tools and greatly improve the cutting speed, while the inevitable unbalance of the spindle system caused by unexpected errors during manufacturing and installation process strongly influences the machining productivity and finish quality of workpieces in high speed operating conditions [5–11]. Therefore, it is necessary to deeply study the dynamic properties of unbalanced machine tool motorized spindle systems. With the low-friction and the convenience in commodity standardization, ball bearings are widely used in high speed motorized spindles [12]. Bearing clearance concerns the contact state between the balls and the inner and outer rings and affects the vibration response of the rotor system [13]. Harsha presented a model for studying the structural vibrations of ball bearing-rotor systems due to radial internal clearance [14]. Sopanen and Mikkola proposed a dynamic model of a ball bearing-rotor system with six degrees of freedom to study the effects of the bearing clearance on the natural frequencies and the vibration responses of the system [15, 16]. Based on it, Gao found that appropriate negative internal clearance helps to reduce the vibration responses of the spindle and improve the stability of the system [17, 18]. Bearing preload could keep the bearing in a negative internal clearance state by eliminating the clearance, but too large preload will produce much frictional heat, leading to the rise of temperature and the decline of bearing life [19]. With the use of the Transfer Matrix Method, Jiang and Mao investigated the variable optimum preload for a machine tool spindle [20]. Alfares and Elsharkawy constructed a mathematical model based on five degrees of dynamic system to study the influences of axial preload of angular ball bearings on the vibration behavior of a grinding machine spindle and calculated the optimum initial axial preload for the system [21].Series of researches on the dynamic performance and the optimal design method of the unbalanced rotor-ball bearing system of motorized spindles were deeply discussed in above works. Motorized spindles are equipped with built-in motors and their output ends are directly connected with tools, and the rotor of the system is acted upon by an additional unbalanced magnetic force except the unbalanced centrifugal force. The unbalanced magnetic force is caused by the nonuniform air gap between the stator and the rotor in operation and affects the dynamic characteristics of the system. In view of this fact, this paper proposes the matrix expression of the magnetic stiffness based on the gap magnetic field energy. Then a dynamic model for high speed motorized spindles is established with the consideration of unbalanced magnetic force, centrifugal force, and nonlinear Hertz contact force. The vibration response and critical speed of the system are systematically calculated and experimentally validated. Finally, the sensitivities of the magnetic, mechanical, and bearing parameters to the critical speed are presented to instruct the dynamic design of unbalanced high speed motorized spindles.


## 2. Dynamic Model of Unbalanced Motorized Spindle System

Figure1 shows a typical motorized spindle system which includes a stator, a spindle shaft (rotor), a cutting tool, a tool holder, and bearing components. The system can be simplified to three disc elements. Considering the motions of the discs along the vertical and horizontal directions, the spindle-bearing system is regarded as a system with six degrees of freedom, as shown in Figure 2. Specifically, the front and rear bearings are treated as springs and dampers in parallel connection, and the magnetic force is treated as springs between the stator and the rotor.Figure 1
A typical high speed motorized spindle system.Figure 2
The simplified model of a motorized spindle system.


### 2.1. Model of Unbalance Magnetic Force

The gap eccentricity of the spindle is shown as in Figure3,o is the inner circle center of stator (the origin of coordinates), o1 is the outer circle center of rotor, and |oo1|=x2+y20.5. c is the centroid of rotor, e is the mass eccentricity of rotor, α is the angle between the x-axis and the circumferential position where the air gap width is equal to δ and β is the angle between the x-axis and the circumferential position where the air gap width is the least.Figure 3
Air gap eccentricity of the rotor in motorized spindles.The built-in motor in high speed machine tool spindle system is generally a three-phase AC induction motor, so the energy of the gap magnetic field of the motor is [22](1)W=RgLg2∫02πΛ0∑n=0∞εncosn⁡α-βFsmcos⁡ωft-pα+Frmcos⁡ωft-pα-φ1-φ22dα.Specifically, the largest component, which isn=0, plays a dominant role; other components, which are n≠0, take different proportion, respectively. Because the effective relative eccentricity ε is far less than 1, expand the high order terms in (1) and take the first three terms, and (1) can be converted into(2)W=RgLgΛ02∫02π1+x2+y22σ2+xσcos⁡α+yσsin⁡α+x2-y22σ2cos⁡2α+xyσ2sin⁡2αFsmcos⁡ωft-pα+Frmcos⁡ωft-pα-φ1-φ22dα,where Rg is the radius of the inner circle of stator; Lg is effective length of rotor; Λ0 is the magnetic conduction of uniform air gap, and Λ0=μ0/kμδ0,μ0 is the air permeability, kμ is the saturation, and kμ=1+δFe/k0δ0,k0 is the calculation coefficient of uniform air gap, δFe is the equivalent air gap of ferromagnetic materials, δ0 is the width of uniform air gap, σ=kμδ0, ωf is the speed of rotating magnetic field, and ωf=2πf/p, f is the current frequency, p is the number of pole-pairs, and Fsm and Frm are the amplitudes of three-phase resultant magnetomotive forces of the stator and the rotor, respectively; φ1+φ2 is the phase angle in which the rotor current lags behind the stator current, and φ1=x1s/r1,φ2=x2s/r2,x1s and x2s are the leakage reactance of per phase winding of the stator and the rotor, respectively; r1 and r2 are the resistances of per phase winding of the stator and the rotor, respectively.Equation (2) can be expressed by (3)W=12VTKeV+VTKe¯,where V=x,yT and Ke is the magnetic stiffness matrix of the gap magnetic field:(4)K11=RgLgΛ02σ2∫02π1+cos⁡2αFsmcos⁡ωft-pα+Frmcos⁡ωft-pα-φ1-φ22dαK12=K21=RgLgΛ02σ2∫02πsin⁡2αFsmcos⁡ωft-pα+Frmcos⁡ωft-pα-φ1-φ22dαK22=RgLgΛ02σ2∫02π1-cos⁡2αFsmcos⁡ωft-pα+Frmcos⁡ωft-pα-φ1-φ22dα.Ke¯ is the vector of the gap magnetic field energy: (5)K1¯=RgLgΛ02σ2∫02πcos⁡α·Fsmcos⁡ωft-pα+Frmcos⁡ωft-pα-φ1-φ22dαK2¯=RgLgΛ02σ2∫02πsin⁡α·Fsmcos⁡ωft-pα+Frmcos⁡ωft-pα-φ1-φ22dα.


### 2.2. Hertz Contact Force Model of Ball Bearings

In the rotor-ball bearing system of a high speed motorized spindle, the inner and outer races of the bearings are fixed to the rotating shaft and the bearing housing, respectively. Balls can be considered to make pure rolling movement between the inner race and the outer race with equal spacing. Therefore for the ball bearing in any time, the elastic deformation associated with the contact point at thejth ball depends on the displacement of rotor and the initial bearing clearance, given by(6)Δj=xbsin⁡θj+ybcos⁡θj-γ,where xb and yb are the displacements at the bearing along x- and y-directions, respectively; θj is the azimuth of thejth ball, and θj=(2π/Nb)j-1+(di/(di+do))ωt, Nb is the number of balls, di is the inner diameter of inner race, and do is the outer diameter of outer race; γ is the initial bearing clearance, which can be determined according to the initial bearing preload [15].Considering that the contact force is nonnegative, the local Hertz contact force and deflection relationship for bearing can be written as [18](7)Fθj=kb·Δj2/3;Δj>00;Δj≤0.k b is contact stiffness which is given as(8)kb=1ki-12/3+ko-12/33/2,where ki=ko=(22/3)·(E/(1-μ))Σρ-1/2·δ∗-3/2, E is the elastic modulus, and μ is the Poisson ratio. The curvature sum Σρ and deformation coefficient δ∗ are obtained from Harris [23].Similar to [24], the contact damping can be written as(9)cb=10-5·kb.By summing the local contact forces, the total restoring force components of the ball bearing along thex- and y-directions are given by(10)Fbx=-cbx˙b-∑j=1NbFθjsin⁡θj;Fby=-cby˙b-∑j=1NbFθjcos⁡θj.


### 2.3. Motional Differential Equations and Stability Analysis of the Spindle System

As the middle part of the spindle system is simplified to a disc element, the gap eccentricity of the motor is considered as uniform. Without regard for the influence of gyroscopic moment, the differential equations governing motions of the motorized spindle systems can be obtained with Newton second law:(11)mb1x¨b1+c1x˙b1-x˙r+k1xb1-xr=-N1·Fbx1mb1y¨b1+c1y˙b1-y˙c+k1yb1-yr=-mb1·g-N1·Fby1mrx¨r+c1x˙r-x˙b1+c2x˙r-x˙b2+k1xr-xb1+k2xr-xb2+K11·xr+K12·yr=Fcx-K1¯mry¨r+c1y˙r-y˙b1+c2y˙r-y˙b2+k1yr-yb1+k2yr-yb2+K21·xr+K22·yr=Fcy-mr·g-K2¯mb2x¨b2+c2x˙b2-x˙r+k2xb2-xr=-N2·Fbx2mb2y¨b2+c2y˙b2-y˙r+k2yb2-yr=-mb2·g-N2·Fby2,where xb1 and yb1, xr and yr, and xb2 and yb2 are the displacements of mass elements distributed at the front bearing, rotor, and the rear bearing along x- and y-directions, respectively. It should be noticed that the variable y is defined along the opposite direction of the gravity. mb1, mr, and mb2 are the masses of the spindle distributed at the front bearing, middle between the two sets of bearings, and the rear bearing, respectively, k1 and k2 are the bending stiffness of the spindle, c1 and c2 are the material damping of the spindle, respectively, and cq=0.001/ω·kq,q=1,2; N1 and N2 are the number of the two sets of bearings, respectively; Fcx=mreω2cos⁡ϕ; Fcy=mreω2sin⁡ϕ, where ω is the angular velocity of rotor, and ω=1-sωf,s is the slip of motor, ϕ is the eccentric angle of rotor mass, and ϕ=ωt.Without the influence of the unbalanced magnetic force, the values of the magnetic stiffness matrix and vector of the gap magnetic field in (11) are zero.Equations (1), (2), (3), (6), (7), (8), (9), (10), and (11) constitute the dynamic model of the unbalanced motorized spindle system. There are coupling items in the model due to the magnetic stiffness; meanwhile the total restoring forces Fbx,Fby are nonlinear functions of vibration amplitudes in x- and y-directions, so the model has strong nonlinear characteristic and the nonlinear vibration theory must be used [25]. The state equations of (11) can be given as(12)F=x˙b1y˙b1x˙ry˙rx˙b2y˙b2-1mb1·c1x˙b1-x˙r+k1xb1-xr+N1·Fbx1-1mb1·c1y˙b1-y˙r+k1yb1-yr+mb1·g+N1·Fby1-1mr·c1x˙r-x˙b1+c2x˙r-x˙b2+k1xr-xb1+k2xr-xb2+K11·xr+K12·yr-Fcx+K1¯-1mr·c1y˙r-y˙b1+c2y˙r-y˙b2+k1yr-yb1+k2yr-yb2+K21·xr+K22·yr-Fcy+mr·g+K2¯-1mb2·c2x˙b2-x˙r+k2xb2-xr+N2·Fbx2-1mb2·c2y˙b2-y˙r+k2yb2-yr+mb2·g+N2·Fby2.The accelerations and velocities are zero in (12) when the spindle system is in equilibrium. According to the first approximate theory of Lyapunov, the motion stability of the nonlinear system is determined by the latent root of the linear approximation system. Expand the state equation (12) at the equilibrium point approximately, and the Jacobi matrix can be obtained. If all Jacobi Matrix Eigen values have negative real parts, the system is asymptotically stable. When part of the Jacobi Matrix Eigen values own negative real parts while the others own positive real parts, the system is unstable. On the other hand, once the value of a real part of the Jacobi Matrix Eigen is zero while the others are not, the system is in a critical state and is starting buckling, and then the critical speed of the spindle could be obtained. Due to the strongly nonlinear characteristic, the equation must be solved with numerical analysis. The Runge-Kutta method is used to calculate (11) to obtain the dynamic responses of the system.


## 2.1. Model of Unbalance Magnetic Force

The gap eccentricity of the spindle is shown as in Figure3,o is the inner circle center of stator (the origin of coordinates), o1 is the outer circle center of rotor, and |oo1|=x2+y20.5. c is the centroid of rotor, e is the mass eccentricity of rotor, α is the angle between the x-axis and the circumferential position where the air gap width is equal to δ and β is the angle between the x-axis and the circumferential position where the air gap width is the least.Figure 3
Air gap eccentricity of the rotor in motorized spindles.The built-in motor in high speed machine tool spindle system is generally a three-phase AC induction motor, so the energy of the gap magnetic field of the motor is [22](1)W=RgLg2∫02πΛ0∑n=0∞εncosn⁡α-βFsmcos⁡ωft-pα+Frmcos⁡ωft-pα-φ1-φ22dα.Specifically, the largest component, which isn=0, plays a dominant role; other components, which are n≠0, take different proportion, respectively. Because the effective relative eccentricity ε is far less than 1, expand the high order terms in (1) and take the first three terms, and (1) can be converted into(2)W=RgLgΛ02∫02π1+x2+y22σ2+xσcos⁡α+yσsin⁡α+x2-y22σ2cos⁡2α+xyσ2sin⁡2αFsmcos⁡ωft-pα+Frmcos⁡ωft-pα-φ1-φ22dα,where Rg is the radius of the inner circle of stator; Lg is effective length of rotor; Λ0 is the magnetic conduction of uniform air gap, and Λ0=μ0/kμδ0,μ0 is the air permeability, kμ is the saturation, and kμ=1+δFe/k0δ0,k0 is the calculation coefficient of uniform air gap, δFe is the equivalent air gap of ferromagnetic materials, δ0 is the width of uniform air gap, σ=kμδ0, ωf is the speed of rotating magnetic field, and ωf=2πf/p, f is the current frequency, p is the number of pole-pairs, and Fsm and Frm are the amplitudes of three-phase resultant magnetomotive forces of the stator and the rotor, respectively; φ1+φ2 is the phase angle in which the rotor current lags behind the stator current, and φ1=x1s/r1,φ2=x2s/r2,x1s and x2s are the leakage reactance of per phase winding of the stator and the rotor, respectively; r1 and r2 are the resistances of per phase winding of the stator and the rotor, respectively.Equation (2) can be expressed by (3)W=12VTKeV+VTKe¯,where V=x,yT and Ke is the magnetic stiffness matrix of the gap magnetic field:(4)K11=RgLgΛ02σ2∫02π1+cos⁡2αFsmcos⁡ωft-pα+Frmcos⁡ωft-pα-φ1-φ22dαK12=K21=RgLgΛ02σ2∫02πsin⁡2αFsmcos⁡ωft-pα+Frmcos⁡ωft-pα-φ1-φ22dαK22=RgLgΛ02σ2∫02π1-cos⁡2αFsmcos⁡ωft-pα+Frmcos⁡ωft-pα-φ1-φ22dα.Ke¯ is the vector of the gap magnetic field energy: (5)K1¯=RgLgΛ02σ2∫02πcos⁡α·Fsmcos⁡ωft-pα+Frmcos⁡ωft-pα-φ1-φ22dαK2¯=RgLgΛ02σ2∫02πsin⁡α·Fsmcos⁡ωft-pα+Frmcos⁡ωft-pα-φ1-φ22dα.


## 2.2. Hertz Contact Force Model of Ball Bearings

In the rotor-ball bearing system of a high speed motorized spindle, the inner and outer races of the bearings are fixed to the rotating shaft and the bearing housing, respectively. Balls can be considered to make pure rolling movement between the inner race and the outer race with equal spacing. Therefore for the ball bearing in any time, the elastic deformation associated with the contact point at thejth ball depends on the displacement of rotor and the initial bearing clearance, given by(6)Δj=xbsin⁡θj+ybcos⁡θj-γ,where xb and yb are the displacements at the bearing along x- and y-directions, respectively; θj is the azimuth of thejth ball, and θj=(2π/Nb)j-1+(di/(di+do))ωt, Nb is the number of balls, di is the inner diameter of inner race, and do is the outer diameter of outer race; γ is the initial bearing clearance, which can be determined according to the initial bearing preload [15].Considering that the contact force is nonnegative, the local Hertz contact force and deflection relationship for bearing can be written as [18](7)Fθj=kb·Δj2/3;Δj>00;Δj≤0.k b is contact stiffness which is given as(8)kb=1ki-12/3+ko-12/33/2,where ki=ko=(22/3)·(E/(1-μ))Σρ-1/2·δ∗-3/2, E is the elastic modulus, and μ is the Poisson ratio. The curvature sum Σρ and deformation coefficient δ∗ are obtained from Harris [23].Similar to [24], the contact damping can be written as(9)cb=10-5·kb.By summing the local contact forces, the total restoring force components of the ball bearing along thex- and y-directions are given by(10)Fbx=-cbx˙b-∑j=1NbFθjsin⁡θj;Fby=-cby˙b-∑j=1NbFθjcos⁡θj.


## 2.3. Motional Differential Equations and Stability Analysis of the Spindle System

As the middle part of the spindle system is simplified to a disc element, the gap eccentricity of the motor is considered as uniform. Without regard for the influence of gyroscopic moment, the differential equations governing motions of the motorized spindle systems can be obtained with Newton second law:(11)mb1x¨b1+c1x˙b1-x˙r+k1xb1-xr=-N1·Fbx1mb1y¨b1+c1y˙b1-y˙c+k1yb1-yr=-mb1·g-N1·Fby1mrx¨r+c1x˙r-x˙b1+c2x˙r-x˙b2+k1xr-xb1+k2xr-xb2+K11·xr+K12·yr=Fcx-K1¯mry¨r+c1y˙r-y˙b1+c2y˙r-y˙b2+k1yr-yb1+k2yr-yb2+K21·xr+K22·yr=Fcy-mr·g-K2¯mb2x¨b2+c2x˙b2-x˙r+k2xb2-xr=-N2·Fbx2mb2y¨b2+c2y˙b2-y˙r+k2yb2-yr=-mb2·g-N2·Fby2,where xb1 and yb1, xr and yr, and xb2 and yb2 are the displacements of mass elements distributed at the front bearing, rotor, and the rear bearing along x- and y-directions, respectively. It should be noticed that the variable y is defined along the opposite direction of the gravity. mb1, mr, and mb2 are the masses of the spindle distributed at the front bearing, middle between the two sets of bearings, and the rear bearing, respectively, k1 and k2 are the bending stiffness of the spindle, c1 and c2 are the material damping of the spindle, respectively, and cq=0.001/ω·kq,q=1,2; N1 and N2 are the number of the two sets of bearings, respectively; Fcx=mreω2cos⁡ϕ; Fcy=mreω2sin⁡ϕ, where ω is the angular velocity of rotor, and ω=1-sωf,s is the slip of motor, ϕ is the eccentric angle of rotor mass, and ϕ=ωt.Without the influence of the unbalanced magnetic force, the values of the magnetic stiffness matrix and vector of the gap magnetic field in (11) are zero.Equations (1), (2), (3), (6), (7), (8), (9), (10), and (11) constitute the dynamic model of the unbalanced motorized spindle system. There are coupling items in the model due to the magnetic stiffness; meanwhile the total restoring forces Fbx,Fby are nonlinear functions of vibration amplitudes in x- and y-directions, so the model has strong nonlinear characteristic and the nonlinear vibration theory must be used [25]. The state equations of (11) can be given as(12)F=x˙b1y˙b1x˙ry˙rx˙b2y˙b2-1mb1·c1x˙b1-x˙r+k1xb1-xr+N1·Fbx1-1mb1·c1y˙b1-y˙r+k1yb1-yr+mb1·g+N1·Fby1-1mr·c1x˙r-x˙b1+c2x˙r-x˙b2+k1xr-xb1+k2xr-xb2+K11·xr+K12·yr-Fcx+K1¯-1mr·c1y˙r-y˙b1+c2y˙r-y˙b2+k1yr-yb1+k2yr-yb2+K21·xr+K22·yr-Fcy+mr·g+K2¯-1mb2·c2x˙b2-x˙r+k2xb2-xr+N2·Fbx2-1mb2·c2y˙b2-y˙r+k2yb2-yr+mb2·g+N2·Fby2.The accelerations and velocities are zero in (12) when the spindle system is in equilibrium. According to the first approximate theory of Lyapunov, the motion stability of the nonlinear system is determined by the latent root of the linear approximation system. Expand the state equation (12) at the equilibrium point approximately, and the Jacobi matrix can be obtained. If all Jacobi Matrix Eigen values have negative real parts, the system is asymptotically stable. When part of the Jacobi Matrix Eigen values own negative real parts while the others own positive real parts, the system is unstable. On the other hand, once the value of a real part of the Jacobi Matrix Eigen is zero while the others are not, the system is in a critical state and is starting buckling, and then the critical speed of the spindle could be obtained. Due to the strongly nonlinear characteristic, the equation must be solved with numerical analysis. The Runge-Kutta method is used to calculate (11) to obtain the dynamic responses of the system.


## 3. Experimental Setup and Measurements

### 3.1. Parameters

To validate the proposed dynamic model, a dynamic operating test was carried out on a DX100A-24000/20-type motorized spindle. The maximum rated speed of the spindle is 24000 rpm. Both the two sets of the bearings are a pair in bearing combination with constant preload, and the front and rear bearings are the angular contact ball bearings of 7006CYTAHQ1 and 7005CYTASP4, respectively, from HRB-BC. Table1 lists the other parameters of the spindle system. It deserves noting that the spindle system can operate with the speed higher than the maximum rated speed in a short time, and the oil dripping rate remains constant in the test to obtain the experimental data with same parameters and conditions.Table 1
Parameters of DX100A-24000/20-type motorized spindle.
Parameter Units Given value m b 1 kg 0.212 m b 2 kg 0.201 m r kg 0.483 k 1 N/mm 12100 d i mm 6.35/6.70 d o mm 6.65/7.05 N b  18/18 k 2 N/mm 9840 s  0.01 e μm 0.879 R g mm 48 L g mm 45 Λ 0 H/mm2 1.468 × 10−9 σ mm 0.856 F s m A 463.4 F r m A 418.3 φ 1 ° 57.2 φ 2 ° 11.3 p  1 μ  0.3 Γ mm −0.0012 δ 0 mm 0.97


### 3.2. Experimental Setup

A dynamic operating test is carried out to obtain the values of vibration response at different speeds. Due to the sharp increase of the vibratory output of the spindle system at the resonant frequency, the first critical speed of the system can be obtained from the variation of the vibration responses of the rotor. To avoid the influence of the thermal displacement, each vibration signal with a speed was collected as quickly as possible once the operating speed is stable, and the interval of each signal collection is more than half an hour.As shown in Figure4, the vibration signals in x- and y-directions at the front end of rotor under work conditions were acquired by using Laser Displacement Sensor (LDS), then transmitted and transformed through the signal collector and analyser UA300, and finally transmitted to the PC to be handled by the signal acquisition procedure compiled by Visual C++ 6.0.Figure 4
Experimental setup.


## 3.1. Parameters

To validate the proposed dynamic model, a dynamic operating test was carried out on a DX100A-24000/20-type motorized spindle. The maximum rated speed of the spindle is 24000 rpm. Both the two sets of the bearings are a pair in bearing combination with constant preload, and the front and rear bearings are the angular contact ball bearings of 7006CYTAHQ1 and 7005CYTASP4, respectively, from HRB-BC. Table1 lists the other parameters of the spindle system. It deserves noting that the spindle system can operate with the speed higher than the maximum rated speed in a short time, and the oil dripping rate remains constant in the test to obtain the experimental data with same parameters and conditions.Table 1
Parameters of DX100A-24000/20-type motorized spindle.
Parameter Units Given value m b 1 kg 0.212 m b 2 kg 0.201 m r kg 0.483 k 1 N/mm 12100 d i mm 6.35/6.70 d o mm 6.65/7.05 N b  18/18 k 2 N/mm 9840 s  0.01 e μm 0.879 R g mm 48 L g mm 45 Λ 0 H/mm2 1.468 × 10−9 σ mm 0.856 F s m A 463.4 F r m A 418.3 φ 1 ° 57.2 φ 2 ° 11.3 p  1 μ  0.3 Γ mm −0.0012 δ 0 mm 0.97


## 3.2. Experimental Setup

A dynamic operating test is carried out to obtain the values of vibration response at different speeds. Due to the sharp increase of the vibratory output of the spindle system at the resonant frequency, the first critical speed of the system can be obtained from the variation of the vibration responses of the rotor. To avoid the influence of the thermal displacement, each vibration signal with a speed was collected as quickly as possible once the operating speed is stable, and the interval of each signal collection is more than half an hour.As shown in Figure4, the vibration signals in x- and y-directions at the front end of rotor under work conditions were acquired by using Laser Displacement Sensor (LDS), then transmitted and transformed through the signal collector and analyser UA300, and finally transmitted to the PC to be handled by the signal acquisition procedure compiled by Visual C++ 6.0.Figure 4
Experimental setup.


## 4. Discussion of the Calculation and Experimental Results

### 4.1. Validation of the Dynamic Model

Figure5 shows the experimental vibration signals of the front end of spindle in y-direction with different speeds. When the rotational speed is 32400 rpm, the vibration value of the spindle is larger than other values with different speeds.Figure 5
Experimental vibration signals of the front end of spindle iny-direction.
(a)
12000 rpm (b)
18000 rpm (c)
32400 rpm (d)
36000 rpmFigure6 shows the experimental vibration displacement curve of the front end of the spindle rotor iny-direction. It can be found from the curve that the first critical speed of the system is about 32400 rpm.Figure 6
Experimental vibration displacement curve of the front end of spindle iny-direction.To discuss the influence of the unbalanced magnetic force on the dynamic behaviors of the system, (12) was studied with and without the magnetic stiffness (MS). The first critical speeds of the spindle system obtained from calculation and experiment are listed in Table 2. As can be seen, considering the effect of MS, the calculated value of the first critical speed decreases and has an error of −6.37% compared with the experimental value. The difference in the first critical speeds between the two calculations is about 14.42%. The difference between the calculation and the measured result in this paper is within 7%, so the data in Table 2 can testify to the accuracy of the proposed dynamic model for motorized spindles. In addition, the calculated value of the first critical speed increases with the number of pole-pairs, which means the MS has a little influence on the system stability in multi-pole-pairs motors.Table 2
First critical speeds of DX100A-24000/20-type motorized spindle.
Number ofpole-pairs Calculation result (rpm) Measured result(rpm) With MS Without MS 1 30336.12 34710.15 32400 2 30391.23 34710.15 3 30487.51 34710.15 4 30621.24 34710.15To study the influence of the MS more directly, the radial displacement of the rotor center is discussed and its value isxr2+yr20.5. Figure 7 shows the theoretical radial displacements of the rotor center. When taking the MS into account, the vibration amplitudes in nonresonance and resonance regions increase; meanwhile the width of the speed region of high vibration amplitudes becomes larger. Combined with the analysis result from Table 2, it can be known that the MS reduces the system stability.Figure 7
Theoretical radial vibration displacement curves of the rotor center.The influence of the radial displacement of the rotor center on the system stability is shown as in Figure8. For the sake of discussion, the relative radial displacement of the rotor center ec is taken and its value is xr2+yr20.5/e. The larger the value of ec is, the lower the critical speed of the system will be, and the downward trend is more gentle, which means when the critical speed of the spindle system is low, a little decrease of the critical speed would lead to more drastic whirling motion. Meanwhile, the ratio between the linear critical angular velocity ωn and the nonlinear critical angular velocity ωc gently increases with the increasing of the value of ec and then sharply decreases. Respectively, ωn presents [{k1+k2+(K11+K12+K21+K22)/4}/mr]0.5 [26] and ωc is the angular velocity form of the first critical speed discussed in Table 2. In a significant extent of the value of ec, the linear critical speed is about 0.65 times that of the nonlinear critical speed.Figure 8
Theoretical influence of the radial displacement of the rotor center on the system stability.
(a)
Critical speed (b)
Angular velocity ratioFigure9 shows the Poincaré mapping of the rotor center iny-direction, which is a typical period-doubling bifurcation. When the angular velocity ωf is at 3000 rad/s, there is a frequency division phenomenon in the system (Figure 9(a)); with the ωf increase to 3180 rad/s, the chaos phenomenon occurs (Figure 9(b)), while the chaos disappears with the inverse bifurcation at 3300 rad/s.Figure 9
Poincaré mapping of the rotor center iny-direction.
(a)
3000 rad/s (b)
3180 rad/s (c)
3300 rad/s


### 4.2. Dynamic Design for Motorized Spindles

To instruct the dynamic design of the spindle system, the influence of system parameters on the first critical speed is discussed and the theoretical results are shown as in Figure10.Figure 10
Theoretical influence of system parameters on critical speed.
(a)
Magnetic parameters (b)
Shaft stiffness (c)
Bearing clearance (d)
Ball number(a) The magnetic parameters presentRgLgΛ0/2σ2 in Figure 10(a), and the unit of the abscissa is the multiple of RgLgΛ0/2σ2. With the increase of the inner radius of stator Rg and the effective length of rotor Lg and the decrease of uniform air gap δ0, the critical speed decreases nonlinearly. When the magnetic parameters are 1.5 times that of the design value, the critical speed is close to the minimum rated speed. So the magnetic parameters are vital to the dynamic design of the spindle system, and their effects on the dynamic characteristic of motorized spindles cannot be ignored. Besides, the increase of the uniform air gap is of advantage to the rotor stability, but the gap cannot be too large and should be optimized.(b) As shown in Figure10(b), with the increase of the shaft stiffness, the first critical speed of the system increases, and the difference between the two calculations decreases, which means that high shaft stiffness can weaken the influence of the MS.(c) Figure10(c) shows the impact of the bearing clearance γ on the critical speed. Preload makes the bearing in a negative clearance state and improves the stability of the spindle system, which also can reduce the effect of MS.(d) Figure10(d) shows that the critical speed rises with the increase of ball number. This is because the increase of ball number leads to the improvement of the support stiffness and the frequency of the parametric vibration for ball bearings and meanwhile undermines the frequency multiplication and harmonic components of the parametric vibration, which benefits the stability of system. Without the consideration of the waviness on the race, the bearings which have more balls can effectively improve the operational stability of the spindle and decrease the influence of MS.Based on the results of Figures10(b), 10(c), and 10(d), it can be known that with the natural properties of the system increase, such as shaft stiffness and support stiffness, the influence of MS to the stability of the system decreases. That means the higher the stability of the system is, the lower the influence of MS to the stability of the system is.


## 4.1. Validation of the Dynamic Model

Figure5 shows the experimental vibration signals of the front end of spindle in y-direction with different speeds. When the rotational speed is 32400 rpm, the vibration value of the spindle is larger than other values with different speeds.Figure 5
Experimental vibration signals of the front end of spindle iny-direction.
(a)
12000 rpm (b)
18000 rpm (c)
32400 rpm (d)
36000 rpmFigure6 shows the experimental vibration displacement curve of the front end of the spindle rotor iny-direction. It can be found from the curve that the first critical speed of the system is about 32400 rpm.Figure 6
Experimental vibration displacement curve of the front end of spindle iny-direction.To discuss the influence of the unbalanced magnetic force on the dynamic behaviors of the system, (12) was studied with and without the magnetic stiffness (MS). The first critical speeds of the spindle system obtained from calculation and experiment are listed in Table 2. As can be seen, considering the effect of MS, the calculated value of the first critical speed decreases and has an error of −6.37% compared with the experimental value. The difference in the first critical speeds between the two calculations is about 14.42%. The difference between the calculation and the measured result in this paper is within 7%, so the data in Table 2 can testify to the accuracy of the proposed dynamic model for motorized spindles. In addition, the calculated value of the first critical speed increases with the number of pole-pairs, which means the MS has a little influence on the system stability in multi-pole-pairs motors.Table 2
First critical speeds of DX100A-24000/20-type motorized spindle.
Number ofpole-pairs Calculation result (rpm) Measured result(rpm) With MS Without MS 1 30336.12 34710.15 32400 2 30391.23 34710.15 3 30487.51 34710.15 4 30621.24 34710.15To study the influence of the MS more directly, the radial displacement of the rotor center is discussed and its value isxr2+yr20.5. Figure 7 shows the theoretical radial displacements of the rotor center. When taking the MS into account, the vibration amplitudes in nonresonance and resonance regions increase; meanwhile the width of the speed region of high vibration amplitudes becomes larger. Combined with the analysis result from Table 2, it can be known that the MS reduces the system stability.Figure 7
Theoretical radial vibration displacement curves of the rotor center.The influence of the radial displacement of the rotor center on the system stability is shown as in Figure8. For the sake of discussion, the relative radial displacement of the rotor center ec is taken and its value is xr2+yr20.5/e. The larger the value of ec is, the lower the critical speed of the system will be, and the downward trend is more gentle, which means when the critical speed of the spindle system is low, a little decrease of the critical speed would lead to more drastic whirling motion. Meanwhile, the ratio between the linear critical angular velocity ωn and the nonlinear critical angular velocity ωc gently increases with the increasing of the value of ec and then sharply decreases. Respectively, ωn presents [{k1+k2+(K11+K12+K21+K22)/4}/mr]0.5 [26] and ωc is the angular velocity form of the first critical speed discussed in Table 2. In a significant extent of the value of ec, the linear critical speed is about 0.65 times that of the nonlinear critical speed.Figure 8
Theoretical influence of the radial displacement of the rotor center on the system stability.
(a)
Critical speed (b)
Angular velocity ratioFigure9 shows the Poincaré mapping of the rotor center iny-direction, which is a typical period-doubling bifurcation. When the angular velocity ωf is at 3000 rad/s, there is a frequency division phenomenon in the system (Figure 9(a)); with the ωf increase to 3180 rad/s, the chaos phenomenon occurs (Figure 9(b)), while the chaos disappears with the inverse bifurcation at 3300 rad/s.Figure 9
Poincaré mapping of the rotor center iny-direction.
(a)
3000 rad/s (b)
3180 rad/s (c)
3300 rad/s


## 4.2. Dynamic Design for Motorized Spindles

To instruct the dynamic design of the spindle system, the influence of system parameters on the first critical speed is discussed and the theoretical results are shown as in Figure10.Figure 10
Theoretical influence of system parameters on critical speed.
(a)
Magnetic parameters (b)
Shaft stiffness (c)
Bearing clearance (d)
Ball number(a) The magnetic parameters presentRgLgΛ0/2σ2 in Figure 10(a), and the unit of the abscissa is the multiple of RgLgΛ0/2σ2. With the increase of the inner radius of stator Rg and the effective length of rotor Lg and the decrease of uniform air gap δ0, the critical speed decreases nonlinearly. When the magnetic parameters are 1.5 times that of the design value, the critical speed is close to the minimum rated speed. So the magnetic parameters are vital to the dynamic design of the spindle system, and their effects on the dynamic characteristic of motorized spindles cannot be ignored. Besides, the increase of the uniform air gap is of advantage to the rotor stability, but the gap cannot be too large and should be optimized.(b) As shown in Figure10(b), with the increase of the shaft stiffness, the first critical speed of the system increases, and the difference between the two calculations decreases, which means that high shaft stiffness can weaken the influence of the MS.(c) Figure10(c) shows the impact of the bearing clearance γ on the critical speed. Preload makes the bearing in a negative clearance state and improves the stability of the spindle system, which also can reduce the effect of MS.(d) Figure10(d) shows that the critical speed rises with the increase of ball number. This is because the increase of ball number leads to the improvement of the support stiffness and the frequency of the parametric vibration for ball bearings and meanwhile undermines the frequency multiplication and harmonic components of the parametric vibration, which benefits the stability of system. Without the consideration of the waviness on the race, the bearings which have more balls can effectively improve the operational stability of the spindle and decrease the influence of MS.Based on the results of Figures10(b), 10(c), and 10(d), it can be known that with the natural properties of the system increase, such as shaft stiffness and support stiffness, the influence of MS to the stability of the system decreases. That means the higher the stability of the system is, the lower the influence of MS to the stability of the system is.


## 5. Conclusions

This paper deals with the problem of analysing the dynamic behaviors of unbalanced high speed motorized spindles supported on ball bearings. An improved dynamic model which takes into account the unbalanced magnetic force is developed for the presented system. The model is studied by using the Lyapunov nonlinear vibration theory. Then, the validation test on a DX100A-24000/20-type motorized spindle is performed. From the calculated and experimental results the following conclusions are drawn.(a) The proposed model accurately predicted the critical speed observed in the experiment and allows exploration of the magnetic force contribution within the context of its assumptions, which can be used for analysing the dynamic properties of high speed machine tool motorized spindle systems.(b) The unbalanced magnetic force in the machine tool motorized spindle system increases the vibration response of the rotor and reduces the critical speed of the system. The influence of the MS on the stability of the system decreases with increasing the number of pole-pairs. With the increase ofec, the critical speed of system decreases, while the ratio ωn/ωc increases and then sharply decreases. The period-doubling bifurcation occurs with the angular velocity ωf being about 3200 rad/s.(c) The system parameters greatly influence the critical speed of the system. The increase of the shaft stiffness and the ball number of bearings is of advantage to the stability, but the increase of the magnetic parameters and bearing clearance would lead to the decrease of the critical speed of the system. If the spindle system has higher natural properties, the influence of MS on the stability of the system will decrease.



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*Source: 2787524-2016-11-08.xml*