# Nonlinear Torsional Vibration Analysis and Nonlinear Feedback Control of Complex Permanent Magnet Semidirect Drive Cutting System in Coal Cutters

Authors: Lianchao Sheng; Wei Li; Gaifang Xin; Yuqiao Wang; Mengbao Fan; Xuefeng Yang
Journal: Complexity
 (2019)

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## Abstract

The semidirect drive cutting transmission system of coal cutters is prone to unstable torsional vibration when the resistance values of its driving permanent magnet synchronous motor (PMSM) are affected by changes in temperatures and tough conditions. Besides, the system has the properties of complex electromechanically coupling such as the coupling between electrical parameters and mechanical parameters. Therefore, in this study, the nonlinear torsional vibration equation was established on the basis of the Lagrange-Maxwell theory. Moreover, in light of the nonlinear dynamic bifurcation theory, the system stability was analyzed by taking the resistance value of power motor as the bifurcation parameter. In addition, the influence of subcritical bifurcation on the torsional vibration was studied by investigating the necessary and sufficient conditions for dynamic Hopf bifurcation and classifying the bifurcation types. At last, in order to suppress destabilizing oscillation induced by Hopf bifurcation, the nonlinear feedback controller was constructed, with the introduction of feedback from the motor velocity as well as the selection of voltage value on theq shaft as the controlled variable. Meanwhile, the three-order normal form and controlling parameters of the system were obtained with the aid of the multiple scales method and the harmonic balance method. In this way, the Hopf bifurcation point was transferred to control the stability of Hopf bifurcation and the amplitude of limit cycle, thus guaranteeing reliable and safe operation of the system. The numerical simulation results indicate that the designed controller boosts an ideal controlling effect.


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## Body

## 1. Introduction

When the tail drum of the permanent magnet semidirect drive cutting transmission system in the coal cutters cuts coals and rocks, due to the uneven intensity of the coal seam, the brittle caving of the coal rock mass, and hard parcels existing, the loads on the drum exhibit the characteristics of randomness, major fluctuations, great impact, etc. [1–3]. Besides, since coal cutters operates in a relatively tough environment, the electrical parameters of its driving motor change with the different temperatures. This not only causes abundant dynamic behaviors of the coupling nonlinear dynamic system, but also leads to the torsional vibration and instability phenomena of the system, thus affecting the working efficiency of coal cutters. The cutting transmission system of permanent magnet semidirect drive in coal cutters, which consists of a permanent magnet synchronous motor (PMSM), a speed reducer, cutting drums, and other components, is a typical electromechanical coupling system [4–6]. The electromechanical coupling mechanism and coupling dynamics are influenced by complicate factors, including mechanics, electromagnetism, and nonlinear dynamics [7–9]. The multivariable and multienergy-domain coupling existing within the complicate electromechanical coupling system is a basic characteristic which the system exhibits during nonstationary processes such as the starting, braking, and load variations. The electromechanical coupling vibration that happens in nonstationary processes will result in defective condition of the equipment and affect the dynamics and stability of the system. It may also give rise to major failure and even safety accidents. Therefore, it is essential to study electromechanical coupling dynamics of the semidirect drive cutting transmission system in coal cutters and the mechanism of torsional vibrations; thus the dynamics of the system will be further optimized.At present, the research on the dynamic properties of cutting units in the coal cutter is mainly focused on the investigation of its whole vibration characteristics based on the virtual prototype technology [10, 11], the influence of gear clearance, meshing stiffness, and gear friction on the system dynamics [12, 13], and forces among gears [14, 15]. Scholars have conducted studies on system dynamics which take “motor-gear-actuator” as the model of transmission structure. The breakdown diagnosis [16, 17] and torsion vibration tests [18, 19] of the transmission system by means of dynamic analysis have become research hot spots. Taking the torsional vibration system of rolling mill with nonlinear friction damping as the research object, Liu et al. [20, 21] analyzed the effects of both subcritical bifurcation and supercritical bifurcation on the system torsional vibration. With the introduction of the motor speed feedback, the nonlinear feedback controller was designed, in which the stator voltages of the drive motor were selected as the control variable, suppressing unstable vibrations for transmission system caused by Hopf bifurcation. The kinetic simulation technology was applied to one-stage gearbox and two-stage gearbox by W. Bartelmus [22], providing more ways for gearbox fault diagnosis. The transient dynamic response of drive motor-gear transmission system in starting process was investigated by T. Khabou et al. [23]. Through the transfer matrix theory and the finite element analyses, Yu et al. [24] studied the propagation of torsional vibration in the shaft which was equipped with periodically attached local resonators. They were also the pioneers in finding the dispersion relation and incidental structure for such structure, confirming the existence of low-frequency gap torsional vibration. Different load fluctuations may result in various rotational speed of the driving motor with the planetary gear. Depending on this case, F. Chaari et al. [25] investigated dynamic behaviors of the planetary gear by considering the fact that variable loads could induce a great change in rotational speed of the motor. Shi et al. [26, 27] illustrated the bifurcation structures and chaotic behaviors when the nonlinear torsional vibration system with nonlinear stiffness and nonlinear friction force was under the external excitation. The stability of undisturbed system was given by means of the stability theory of equilibrium positions of Hamiltonian systems. And chaotic behaviors under periodic disturbance were detected by using Melnikov theory. However, from the above, it can be seen that most public literatures attach high attention on the single aspect, either from mechanical perspective or from electrical aspect which cannot present a thorough insight into the mechanism of torsional vibration to provide the corresponding control methods. One reason to explain this limitation is the complex energy transmission between electromagnetic energy of the motor and kinetic energy of the machinery. Therefore, some scholars have started to study the reasons of torsional vibration and push for controlling methods from the view of electromechanical coupling. According to Xu et al. [28], the nonlinear electromechanically coupling dynamic equation of the driving system was given by the analysis of the nonlinear interactive magnetic forces in the electromechanical system in order to further study on the bifurcation and chaotic motions. The influence of the electromagnetic stiffness and the damping coefficient on the electromechanical system was generated by Tomasz Szolc et al. [29], where the rotating machine under dynamic coupling effect was modeled. Concerning those electromechanical coupling system of rolling mills with nonlinear friction force, the dynamic equation of its torsional vibration was set up by Liu et al. [30] through the adoption of electromechanical analytical dynamic method.In this paper, the electromechanical coupling transmission system of coal cutters under the coupling effect of electrical parameters and mechanical parameters is studied, where the dynamic model of its nonlinear coupling torsional vibration is established with reference to the Lagrange-Maxwell equation. Besides, based on numerical and analytical methods, the necessary and sufficient conditions are presented with various the stator resistance values of PMSM. Furthermore, the Hopf bifurcation types are determined, which makes it possible to analyze their influence on the torsional vibration of the system. Aimed at suppressing unstable vibration, the voltage value of the motor on the q-axis is taken as control parameter, in which the velocity feedback is introduced; thus, the feedback controller under nonlinear states is designed. Finally, the methods of multiple scales and harmonic balance are employed to obtain the third-order normal form for the system and its controlling parameters, by which the bifurcation point is transferred, enhancing the system stability and decreasing the limit cycle amplitudes.


## 2. Electromechanical Coupling Dynamic Model

The permanent magnet semidirect drive cutting transmission system in coal cutters which incorporates a variety of subsystems serves as a typical complex electromechanical coupling system. The electromechanical coupling of such system mainly refers to the fact that the electromagnetic parameters of the PMSM are coupled with the mechanical parameters of the gear transmission system and the load system. The conversion of motor electrical energy requires air gap magnetic field. Unlike a three-phase asynchronous motor, which generates a magnetic field by passing current through a motor winding, a PMSM generates a magnetic field by a permanent magnet. In order to facilitate the establishment of an electromechanical coupling dynamics model, the latter part of the gear transmission system is equivalent to the end of the elastic connection shaft. The simplified model is shown in Figure1.Figure 1
Schematic diagram of electromechanical coupling system in coal cutter.Under the assumptions that (I) the core saturation, the eddy current, and hysteresis are ignored; (II) air gap distribution is uniform and the stator windings are star-connected; (III) no damping effect is on the rotor and the permanent magnet; (IV) the back electromotive force waveform is a sine wave, the dynamic equations of the system are established, as shown in the simplified model of Figure1.Based on the basic principles of electromechanical analysis dynamics and Lagrange-Maxwell equation, the mathematical model is established. The generalized coordinates of the system are first determined as shown in Table1.Table 1
Generalized coordinates of electromechanical system.
Generalized coordinates Stator Motor rotation angle Mechanical system j = 1 j = 2 j = 3 j = 4 j = 5 q j e a e b e c θ 1 θ 2 q ˙ j i a i b i c θ ˙ 1 θ ˙ 2 Q j u a u b u c - T LThe specific calculation method ofTL is shown in the literature [3]. The system kinetic energy E is given by(1)E=12J1θ˙12+12J2θ˙22J 1 is the moment of inertia of the rotor in the PMSM and J2 is the equivalent mass moment of inertia of the driven mechanical part reduced to the motor rotor rotation axis.The system magnetic energyWH is expressed as follows:(2)WH=WH1+WH2=12Laia2+12Lbib2+12Lcic2+Hiaib+Hibic+Hiaic+iaψfcos⁡θ1+ibψfcos⁡θ1-23π+icψfcos⁡θ1+23πThe magnetic energyWH of the PMSM includes two parts: WH1 is the magnetic energy generated by the stator current; WH2 is the magnetic energy generated by stator current with the flux which is produced by rotor in the stator. ia, ib, and ic are the current at both ends of each winding. L and H are the self-inductance and mutual inductance of the stator three-phase windings respectively. θ1 is the rotor position angle, and ψf is the flux generated by the permanent magnet.The system potential energyV can be derived as follows:(3)V=12kθ1-θ22The Lagrange functionL of the system is calculated as follows:(4)L=E+WH-V=12J1θ˙12+12J2θ˙22+12Laia2+12Lbib2+12Lcic2+Hiaib+Hibic+Hiaic+iaψfcos⁡θ1+ibψfcos⁡θ1-23π+icψfcos⁡θ1+23π-12kθ1-θ22The system dissipation functionF can be expressed as follows:(5)F=F1+F2=12Raia2+12Rbib2+12Rcic2+12Cθ˙1-θ˙22F 1 is the dissipation function of the electromagnetic system.F2 is the dissipation function of the mechanical system. Ra, Rb, and Rc are the three-phase resistance of the PMSM, and Ra=Rb=Rc=R.C is the viscous damping coefficients of the shaft.The frictional resistance torque caused by the nonlinear friction damping at the end of semidirect drive transmission system in coal cutter takes a widely existing form of nonlinear sliding frictional torque.(6)fθ˙2=κ+γθ˙2+χθ˙22Substituting (4) and (5) into the system’s Lagrange-Maxwell equation, the result is shown as follows:(7)ddt∂L∂q˙j-∂L∂qj+∂F∂q˙j=QjFor the stator windingA(j=1), the specific expansion form is shown as follows:(8)∂L∂q1=0,∂L∂q˙1=Lia+Hib+Hic+ψfcos⁡θ1ddt∂L∂q˙1→ddt∂L∂ia=Ldiadt+Hdibdt+Hdicdt+ddtψfcos⁡θ1∂F∂q˙1→∂F∂ia=RaiaQ1=ddt∂L∂q˙1-∂L∂q1+∂F∂q˙1,ua=Q1So the voltage equation of the stator windingA(j=1) can be expressed as follows:(9)ua=Q1=ddt∂L∂q˙1-∂L∂q1+∂F∂q˙1=Ldiadt+Hdibdt+Hdicdt+ddtψfcos⁡θ1+RaiaSimilarly, the voltage equation of the stator windingB(j=2) is given by(10)ub=Q2=ddt∂L∂q˙2-∂L∂q2+∂F∂q˙2=Ldibdt+Hdiadt+Mdicdt+ddtψfcos⁡θ1-23π+RbibThe voltage equation of the stator windingC(j=3) is given by(11)uc=Q3=ddt∂L∂q˙3-∂L∂q3+∂F∂q˙3=Ldicdt+Hdiadt+Hdibdt+ddtψfcos⁡θ1+23π+RcicThe motion equation of the motor rotation angle(j=4) is formulated,(12)J1dθ˙1dt=-iaψfsin⁡θ1-ibψfsin⁡θ1-23π-icψfsin⁡θ1+23π-kθ1-θ2-Cθ˙1-θ˙2The motion equation of the mechanical system(j=5) is generated,(13)J2dθ˙2dt=-kθ1-θ2+Cθ˙1-θ˙2+TL+κ+γθ˙2+χθ˙22The mathematical model of PMSM inABC three-phase stationary coordinate system is shown in the following equation:(14)uaubuc=R000R000Riaibic+ddtLHHHLHHHLiaibic+ddtψfcos⁡θ1ψfcos⁡θ1-23πψfcos⁡θ1+23πThe system dynamics equation can be written as follows:(15)Ladiadt+Hdibdt+Hdicdt-ψfθ˙1sin⁡θ1+Ria=uaLbdibdt+Hdiadt+Hdicdt-ψfθ˙1sin⁡θ1-23π+Rib=ubLcdicdt+Hdiadt+Hdibdt-ψfθ˙1sin⁡θ1+23π+Ric=ucJ1θ¨1+Cθ˙1-θ˙2+Kθ1-θ2=-iaψfsin⁡θ1-ibψfsin⁡θ1-23π-icψfsin⁡θ1+23πJ2θ¨2-Cθ˙1-θ˙2-Kθ1-θ2=TL+κ+γθ˙2+χθ˙22From (15), as a variable-coefficient differential equation, the established mathematical model is more complex. In order to simplify the equation and describe the motion state conveniently, theABC three-phase stationary coordinate system is converted to thedq axis coordinate system.The principle of coordinate conversion is shown in Figure2. Firstly, theABC three-phase coordinate system needs to be converted to the αβ plane stationary coordinate system. Then, the αβ plane stationary coordinate system is converted to thedq axis coordinate system. Finally the coordinate conversion equation is written as follows: (16)C3s/2r=23cos⁡θcos⁡θ-2π3cos⁡θ+2π3-sin⁡θ-sin⁡θ-2π3-sin⁡θ+2π3121212Figure 2
Principle of coordinate transformation.The electromechanical coupling dynamic equation of the system is shown as follows:(17)I˙d=-RL-HId+udL-H+ω1IqI˙q=-RL-HIq+uqL-H-6ψf2L-Hω1-ω1Idα˙=ω1-ω2ω˙1=1J1-Cω1-ω2-Kα-6ψf2Iqω˙2=1J2Cω1-ω2+Kα+κ+γω2+χω22+TL


## 3. Hopf Bifurcation Analysis of Electromechanical Coupling System

Takingk1=-R/L-H, k2=-6ψf/2L-H, and k3=-6ψf/2J1, IdIqαω1ω2T is expressed with x1x2x3x4x5T. Then the equilibrium point of (17) can be transferred to the origin of coordinates by proper linear transformation. Without loss of generality, the dynamic characteristics of the equilibrium point of the system at the origin are studied, and the Jacobian matrix of the system at the origin can be expressed as follows:(18)A0,R=k100000k10k200001-10k3-KJ1-CJ1CJ100KJ2CJ2γ-CJ2The stability of the system at the equilibrium point is determined by the real part of the eigenvalues of the Jacobian matrixA0,R. If the eigenvalues of Jacobian matrix A0,R are all negative, then the system is asymptotically stable at the equilibrium point; If there is a positive real part in the eigenvalues of A0,R, then the system is unstable at the equilibrium point and easily induces instability oscillation; if there is a pure imaginary root in the eigenvalue of A0,R, then the higher order terms need to be analyzed. At this time, the system has rich dynamic behavior.The characteristic equation of the system Jacobian matrixA0,R can be expressed as follows:(19)λ5+p1λ4+p2λ3+p3λ2+p4λ+p5=0In (19),(20)p1=CJ1+C-γJ2-2k1,p2=K+J2k12+2γk1-2Ck1-J2k2k3J2+K-2k1CJ1-γCJ1J2p3=Ck12-2Kk1J1+Ck12+J2k1k2k3-γk12-2Kk1-C-γk2k3J2+2k1γC-γKJ1J2,p4=Kk12J1+Kk12+C-γk1k2k3-Kk2k3J2+2Kk1γ-k12γCJ1J2,p5=Kk1k2k3J2-γKk12J1J2The Hurwitz determinant can be constituted by the coefficientpi and be expressed in the following form.(21)Δi=p110⋯0p3p2p1⋯0p5p4p3⋯p1⋮⋮⋮⋮p2i-1p2i-2p2i-3⋯piIfi>5, then pi =0.R=R0 is defined as the Hopf bifurcation point of the original system. According to the Hurwitz determinant, the necessary and sufficient conditions for Hopf bifurcation in the system can be expressed as follows:(22)piR0>0i=1,2,3,…,5ΔiR0>0i=1,2,3Δ4R0=0dΔ4RdRR=R0≠0Let the pure imaginary root of the system be±ω0i. The normalized left and right characteristic vectors of the matrix A(0,R) corresponding to the eigenvalue ω0i are denoted by U and V, respectively.(23)UA=ω0iUAV=ω0iVUV=1Let(24)Ψ=Re-UfxxxVVV∗+2UfxxVA-10fxxVV∗+UfxxV∗×A0-2iω0I-1fxxVVV ∗ is the conjugate complex number of V.(25)A0=A0,RR=R0,fxxxVVV∗=∂∂x∂∂x∂fx,R∂x×V×V×V∗R=R0,x=0.According to the positive or negative values ofΨ, the stability of the periodic solution during the Hopf bifurcation period can be determined. If Ψ>0 the bifurcation period of the system is asymptotically stable, and the limit cycle is stable. The Hopf bifurcation occurring at this time is supercritical bifurcation. If Ψ<0, the bifurcation period of the system is unstable, and the limit cycle is unstable. The Hopf bifurcation occurring at this time is subcritical bifurcation.The mechanical and electrical parameters of the permanent magnet semidirect drive system in the coal cutter are taken as follows:L=2.3×10∧-3H,H=6.2×10∧-5H,K=400000N·m/rad,J1=J2=100kg·m2. ψf=3.8Wb. Numerical simulation analysis of system model is carried out in Matlab2015b. The numerical simulation results show that whenR=R0=0.09Ω, Hopf bifurcation occurs in the system, which could cause system instability and oscillation. SubstitutingR0 into (24), Ψ=-0.8962<0, so the periodic orbit is unstable and the Hopf bifurcation is a complex subcritical bifurcation.With different resistance values of the PMSM in the neighborhood of the subcritical Hopf bifurcation point, the motion state of the input elastic torque shaft of permanent magnet semidirect drive electromechanical coupling system is shown as Figures3–6. WhenR=0.1Ω which is away from the limitR0=0.09Ω of instability, the motion state of the input elastic torque shaft is stable and is shown as Figure 3. WhenR=0.094Ω which is near the limitR0=0.09Ω of instability, there are two different trajectories determined by the initial conditions. When the initial value is closer to the equilibrium point, taking [0.10.10.10.10.1], the motion state of the input elastic torque shaft is stable and is shown as Figure 4; when the initial point is farther from the initial point, taking [0.70.70.70.70.7], the motion state of the input elastic torque shaft is unstable and is shown as Figure 5. The amplitude of limit cycle is large. The system becomes unstable which could cause system instability oscillation. WhenR is less thanR0, for any initial condition, the motion state of the input elastic torque shaft is divergent and unstable. TakingR=0.085Ω as an instance, the system is in a diverging state and as Figure 6.Figure 3
When the motor resistanceR= 0.1Ω, initial value = [0.10.10.10.10.1], system motion state: (a) time history diagram; (b) phase diagram.
(a) (b)Figure 4
When the motor resistanceR = 0.094Ω, initial value =[0.10.10.10.10.1], system motion state: (a) time history diagram; (b) phase diagram.
(a) (b)Figure 5
When the motor resistanceR = 0.094Ω, initial value =[0.70.70.70.70.7], system motion state: (a) time history diagram; (b) phase diagram.
(a) (b)Figure 6
When the motor resistanceR = 0.085Ω, initial value =[0.10.10.10.10.1], system motion status: (a) time history diagram; (b) phase diagram.
(a) (b)It can be found through the above analysis that when the system makes subcritical bifurcation, the behavior of the system is more complicated. Under normal circumstances, the initial conditions will have an important impact on the stability of the system. When the motor resistanceR is close to or smaller than the Hopf bifurcation point, a large amplitude unstable oscillation will burst, and the system will suddenly burst from stable to unstable. Therefore, when subcritical Hopf bifurcation occurs in the system, a sudden violent torsional oscillation will be caused on the input elastic torque shaft of the permanent magnet semidirect drive electromechanical coupling system in coal cutter, which will do harm to the safe and reliable operation of the system. In order to avoid this phenomenon, it is necessary to propose a control method for Hopf bifurcation in the above system and suppress the occurrence of subcritical bifurcation by shifting the bifurcation point or reducing the amplitude of vibration to avoid the occurrence of destructive oscillations.


## 4. Nonlinear Feedback Control of Electromechanical Coupling System

The vector control method with ofId= 0 is adopted, and the q-axis voltage of the PMSM stands for a controlled quantity. A nonlinear state feedback controller is constructed as follows by introducing the motor speed feedback.(26)uq=Kcω1+Knω13K c is a linear state feedback parameter. Kn is a nonlinear state feedback parameter.Since the vector control method withId=0 is used, the bifurcation characteristics is no longer affected by the first equation of the system. The system state equation can be written as follows:(27)x˙2=-RL-Hx2+Kcx4+Knx43L-H-6ψf2L-Hx4x˙3=x4-x5x˙4=1J1-Cx4-x5-Kx3-6ψf2x2x˙5=1J2Cx4-x5+Kx3+κ+γx5+χx52+TLAccording to the state equation, it can be found that the equilibrium point of the system remains unchanged after adding the nonlinear state feedback controller.Letkc=Kc/L-H; let the Jacobian matrix of the system be expressed as follows:(28)A′0,R=k10kc+k20001-1k3-KJ1-CJ1CJ10KJ2CJ2γ-CJ2The characteristic equation of the Jacobian matrix is developed as(29)λ4+p1′λ3+p2′λ2+p3′λ+p4′=0In (29),(30)p1′=CJ1+C-γJ2-k1,p2′=K-Ck1J1+K-Ck1+k1γJ2-CγJ1J2-k2k3+k3kcp3′=-Kk1J1+k2k3γ+kck3γ-Kk1-Ck2k3-Ck3kcJ2+Ck1γ-KγJ1J2,p4′=-Kk2k3-Kk3kcJ2+Kk1γJ1J2The Hurwitz determinant is constituted by the characteristic equation coefficientpi′ and shown as follows:(31)Δi′=p1′10⋯0p3′p2′p1′⋯0p5′p4′p3′⋯p1′⋮⋮⋮⋮p2i-1′p2i-2′p2i-3′⋯pi′Ifi>4, then pi′=0. R=R0∗ is defined as the Hopf bifurcation point of the original system. The necessary and sufficient conditions for Hopf bifurcation in the system can be expressed in terms of the Hurwitz determinant,(32)pi′R0∗>0i=1,2,3,4Δi′R0∗>0i=1,2Δ4′R0∗=0dΔ4′RdRR=R0∗≠0According to the calculation results of the system Hurwitz determinant, it is found that the Hopf bifurcation point can be transferred with different values of the parameterKc for a larger stable interval. To be more specific, when Kc=0.5, the bifurcation point is transferred to R0∗=0.079Ω, then the minimum value of the stable area of the system changes from 0.09 to 0.079; when Kc=1, the bifurcation point is transferred to R0∗=0.0679Ω, and the minimum value of the stable area of the system reduces to 0.0679 from 0.09; when Kc=1.5, the bifurcation point is transferred to R0∗=0.0565Ω, and the minimum value of the stable area of the system decreases from 0.09 to 0.0565. According to the stable interval corresponding to different Kc values, it can be observed that the stable area of the controlled system is significantly larger than the original system. And when the system undergoes different temperatures, the stable area of the permanent magnet semidirect drive electromechanical coupling transmission system in coal cutter will expand.For a better understanding on system’s Hopf bifurcation, nonlinear analysis is performed on the system to realize the stability control of the Hopf bifurcation periodic solution and the amplitude control of the limit cycle. Considering subcritical bifurcation pointR0∗=0.0565Ω and Kc=1.5 as an instance, let R=R0∗+η, η is the perturbation amount of the bifurcation parameter R0∗. When the perturbation quantity η=0, the eigenvalues of the system Jacobian matrix are λ1,2=±6.1268i, λ3=-26.4589, and λ4=-0.0056, and the eigenvectors corresponding to the eigenvalue are (u+vi,u-vi,U1,U2). The system transformation matrix can be written as T=uvU1U2. The following linear transformation is performed for (27):(33)X=TY,Y=y1y2y3y4TThe nonlinear standard equation of the system at the critical point can be expressed as follows:(34)Y˙=JY+hYJ is the Jordan standard form of the linearization matrix of the nonlinear rotation system. h(x) is a nonlinear term.(35)J=0ω000-ω000000-α30000-α4(36)hx=0.0151kn-0.0179y1-0.0043y2+0.0009y3-0.0179y43+26.8519κ+TL+χ0.0155y1+0.0114y2-0.0179y420.0183kn-0.0179y1-0.0043y2+0.0009y3-0.0179y43+6.6261κ+TL+χ0.0155y1+0.0114y2-0.0179y420.9587kn-0.0179y1-0.0043y2+0.0009y3-0.0179y43+1.15396κ+TL+χ0.0155y1+0.0114y2-0.0179y420.0262kn-0.0179y1-0.0043y2+0.0009y3-0.0179y43-28.3907κ+TL+χ0.0155y1+0.0114y2-0.0179y42Equation (34) can be expanded as follows:(37)y˙1=ω0y2+h1yy˙2=-ω0y1+h2y(38)y˙3=-α3y3+h3y(39)y˙4=-α4y4+h4yFrom (37)~(39) and on the basis of the method of multiple scales, the normal form of the nonlinear system can be calculated by introducing the following new variables:(40)Tk=εktk=0,1,2,…That is,T0=t,T1=εt,T2=ε2t,…. ε is a small parameter. So the derivative to t becomes an expanded form of the partial derivative to Tk.(41)ddt=dT0dt∂∂T0+dT1dt∂∂T1+⋯=D0+εD1+⋯d2dt2=D02+2εD0D1+ε2D12+2D0D2+⋯D i denotes ∂/∂Ti, the solution of the equation can be expressed as follows,(42)yit,ε=εyi1T0,T1,T2,…+ε2yi2T0,T1,T2,…+⋯Substituting (41) and (42) into (35), according to the perturbation method, the each order equations of each order of ε are established as follows:ε1: (43)D0y11=ω0y21D0y21=-ω0y11(44)D0y31=-α3y31(45)D0y41=-α4y41ε2:(46)D0y12=ω0y22-D1y11+h12y1D0y22=-ω0y12-D1y21+h22y1(47)D0y32=-α3y32+h32y1(48)D0y42=-α4y42+h42y1ε3:(49)D0y13=ω0y23-D1y12-D2y11+h13y1,2D0y23=-ω0y23-D1y22-D2y21+h23y1,2(50)D0y33=-α3y33+h33y1,2(51)D0y43=-α4y43+h43y1,2In order to obtain the first-order approximate solution of system (34), according to the relationship between the two equations in (43), the following can be obtained:(52)D02y11+ω02y11=0The first-order approximate solution ofy1 can be solved as follows:(53)y11=rT1,T2,…cos⁡ω0T0+φ1T1,T2,…=R1T1,T2,…ejω0T0+ccIn (53), R1T1,T2,…=rT1,T2,…/2ejφT1,T2,….r and φ represent the amplitude and phase of the first-order approximate periodic solution of y1, respectively. Similarly, the first-order approximate solution of y2 can be expressed as follows:(54)y21=-rT1,T2,…sin⁡ω0T0+φT1,T2,…The asymptotically stable solutionsyj1=0,j=3, 4, which can be found clearly by (44) and (45) in the ε1 term.The relationship between the two equations in (46) is used to develop the second-order approximate solution for y as follows:(55)D02y12+ω02y12=-D0D1y11-ω0D1y21+D0h12+ω0h22The second-order approximate solution of y can be expressed as follows:(56)yi2=∑n=02Eicos⁡nθ+Fisin⁡nθSubstitutingyi1 and yi2 into (55), n=1,2, the expressions for the trigonometric functions cos⁡nθ and sin⁡nθ, n=1,2,3, can be obtained. Eliminating systemsecular terms, the second-order approximate solution of y and the D1r, D1φ can be obtained.Similarly, according to the relationship between the two equations in (49), the equation can be rewritten as follows:(57)D02y13+ω02y13=-D0D2y11-ω0D2y21-D0D1y12-ω0D1y22+D0h13y1,2+ω0h23y1,2Similarly, the third-order approximate solution ofy can be expressed as follows:(58)yi3=∑n=03Picos⁡nθ+Qisin⁡nθThe third-order approximate solution ofy and the D2r, D2φ can be achieved through the harmonic balance method.According toD0r, D1r, D2r and D0φ, D1φ, D2φ obtained from the synthesis of nonlinear vibration theory, the third-order normal form in the polar coordinate of system can be obtained.(59)r˙=D0r+D1r+D2r=-3.3722ηr+-0.3277Kn+0.0029r3θ˙=ωc+D0φ+D1φ+D2φ=6.1268+4.0868η+0.2001Kn+0.00059r2The opening item in (59) is shown as follows:(60)δr=12∂2y˙1∂y1∂η+∂2y˙2∂y2∂η=-3.3722δθ=12∂2y˙1∂y2∂η-∂2y˙2∂y1∂η=4.0868The necessary and sufficient condition for the occurrence of supercritical Hopf bifurcation in the system is listed as follows:(61)-0.3277Kn+0.0029<0That is,(62)Kn>0.0088(63)r=-3.3722η0.3277Kn-0.0029The numerical simulation for the limit cycle which is produced in the neighborhood of the Hopf bifurcation point of the controlled system verifies the effectiveness of the designed linear feedback controller and nonlinear controller on the Hopf bifurcation transmission, the limit cycle stability, and amplitude adjustment. Taking the linear controller control parameterKc=1.5 and the bifurcation parameterR=0.085Ω as an example, the system time history diagram and phase diagram are drawn as follows when there is no nonlinear feedback controller installed.Comparing Figure6 with Figure 7, it can be found that, after adding the linear controller and the drive motor resistanceR=0.085, the original system runs from chaotic into a smooth state at the equilibrium point, supporting the idea that the linear controller could effectively expand the stable interval in the system.Figure 7
WhenR = 0.085Ω, Kc=1.5, and Kn=0, initial value =[0.10.10.10.1], system motion status: (a) time history diagram; (b) phase diagram.
(a) (b)When the nonlinear controller is not added, the subcritical Hopf bifurcation still occurs near the bifurcation point of the original system. TakingR=0.0566Ω as an example, when the initial value takes the smaller value [0.10.10.10.1], the system works in steady state. With other parameters unchanged, Hopf bifurcation occurs in the system when the initial value is increased to [0.70.70.70.7]. The results of the numerical simulation are shown in Figures 8 and 9.Figure 8
WhenR = 0.0566Ω, Kc=1.5, and Kn=0, initial value =[0.10.10.10.1], system motion status: (a) time history diagram; (b) phase diagram.
(a) (b)Figure 9
WhenR = 0.0566Ω, Kc=1.5, and Kn=0, initial value =[0.70.70.70.7], system motion status: (a) time history diagram; (b) phase diagram.
(a) (b)Without adding a nonlinear controller, the system subcritical Hopf bifurcation still occurs at the point of bifurcation. The system will produce instability and oscillation, which will damage the system, affect the system work efficiency, and even cause security accidents. Therefore, it is necessary to install nonlinear controller. Taking nonlinear controller parameterKn=0.5, motor resistanceR=0.0566Ω, and initial value =[0.70.70.70.7], numerical simulation results are shown in Figure 10.Figure 10
WhenR = 0.0566Ω, Kc=1.5, and Kn=0.5, initial value =[0.70.70.70.7], system motion status: (a) time history diagram; (b) phase diagram.
(a) (b)From Figure10, it is suggested that, with the nonlinear controller installed, the system operates from unstable state into a stable state when motor resistanceR=0.0566Ω and initial value =[0.70.70.70.7], indicating that the designed nonlinear controller has a sound control effect.When the nonlinear controller is added to the controlled system, the system supercritical Hopf bifurcation is generated at the neighborhood of the Hopf bifurcation pointR0∗. When the bifurcation parameterR=0.05Ω<R0∗, the stable limit cycle is generated near the equilibrium point, as shown in Figures 11 and 12. It effectively avoids the more harmful subcritical destabilizing oscillations with greater harm. WhenR is the same, the amplitude of the stable limit cycle can be controlled by changing the parameterKn. Comparing Figure 11 with Figure 12, we can see that when Kn=10, the system limit cycle amplitude is obviously smaller than it when Kn=0.05. Also as the Kn increases, the limit cycle amplitude of the system decreases. Although there is a certain error between the limit cycle amplitude obtained by numerical simulation and the analytical calculation in Figures 11 and 12, the variation trend of the limit cycle amplitude is consistent. Therefore, the amplitude of the system oscillation can be reduced by increasing the feedback coefficient Kn. The damage degree of the torsional vibration of the semidirect drive transmission system in coal cutter is reduced.Figure 11
WhenR = 0.05Ω, Kc=1.5, and Kn=0.5, initial value =[0.10.10.10.1], system motion status: (a) time history diagram; (b) phase diagram.
(a) (b)Figure 12
WhenR = 0.05Ω, Kc=1.5, and Kn=10, initial value =[0.10.10.10.1], system motion status: (a) time history diagram; (b) phase diagram.
(a) (b)


## 5. Conclusions

As the three-phase asynchronous motor has been replaced by the PMSM, in which the intermediate drive devices are shortened, the permanent magnet semidirect drive cutting transmission system of coal cutters has been composed, minimizing the breakdown rate and improving the system stable performance greatly. When the temperature changes or the working conditions become worse, its unstable vibration may appear caused by resistance value of PMSM. On the basis of this and with its complex electromechanical coupling characteristics combined, the dynamics equation of nonlinear torsional vibration system is set up, analyzing the Hopf bifurcation both qualitatively and quantitatively. In addition, given the q-axis as the controlling variable, the nonlinear speed feedback controller is presented, eliminating the torsional vibration effectively. The results are demonstrated as follows:(1) Coal cutters perform in a relatively adverse environment, which may bring a change in electrical parameters. As a result, subcritical Hopf bifurcation may occur in the main driving system, causing the system extremely vibration which may exert a negative effect on the system performance.(2) The control effect of the nonlinear controller is verified by numerical simulation. On the one hand, the linear part can expand the stable region of the system. On the other hand, the nonlinear part can reduce subcritical bifurcation phenomenon as well as the limit cycle amplitudes.(3) The amplitudes of a stable limit cycle decrease along with the increase of the nonlinear parameters. Since the proposed controller may implement effective control on the torsional vibration in the scraper conveyor of main power system electrically, a safe and reliable guarantee is provided for the application of high-power permanent magnet synchronous motors, an expectation of the utilizing in the area of large-scale mechanical equipment.



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*Source: 9359218-2019-05-20.xml*