Dynamic Characteristics of Encased Differential Gear Train with Journal Bearing

Yang, Jie; Yue, Yanjiong; Zhu, Rupeng; Chen, Weifang; Li, Miaomiao

doi:https://doi.org/10.1155/2020/2436191

Mathematical Problems in Engineering

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Abstract Introduction Analysis Conclusions Data Availability Conflicts of Interest Acknowledgments References Copyright Related Articles

Research Article | Open Access

Volume 2020 | Article ID 2436191 | https://doi.org/10.1155/2020/2436191

Dynamic Characteristics of Encased Differential Gear Train with Journal Bearing

Jie Yang,¹Yanjiong Yue,²Rupeng Zhu,¹Weifang Chen,¹and Miaomiao Li¹

Academic Editor: Damijan Markovic

Received31 Oct 2019

Accepted23 Mar 2020

Published20 Apr 2020

Abstract

Taking the marine encased differential gear train as an example, the relationship between the journal bearing parameters and the meshing force of the transmission system is analyzed. In this paper, the dynamic model of the encased differential gear train with journal bearing is established considering the factors of time-varying meshing stiffness and comprehensive transmission error. In this dynamic model, four stiffnesses and four damping coefficients are applied to characterize the asymmetry and interaction of the oil film stiffness and damping of planet bearing. The system responses are calculated by the Fourier series numerical algorithm. The results show that the introduction of journal bearing in encased differential gear train can contribute to gearbox vibration reduction. Moreover, the planet bearing parameters (e.g., clearance-to-radius ratio and eccentricity ratio) of the differential stage affect the meshing forces of both the differential and encased stages. In addition, the influence of the planet bearing parameters of the encased stage on the meshing force of the encased stage is more obvious than that of the differential stage. This work may develop a theoretical analysis framework for the design and manufacture of marine transmission systems in the future.

1. Introduction

The compound planetary gear train, which performs well in compactness, high power density, and large torque-to-weight ratio, is widely used in ship, helicopter, wind turbine, etc. As for heavy machinery transmission systems, journal bearings typically support the carrier and planet in compound planetary gear train, and their stiffness and damping are unequal in all directions [1]. Vibration noise is an important factor affecting the stability and reliability of the gearbox. Studying the dynamic characteristics of a compound planetary gear train may help to reduce the vibration noise.

Some researchers [2–5] focused on the construction of the gear-rotor dynamics model. Using the finite element method, Baguet and Jacquenot [2] established a gear-rotor-bearing coupling model, in which the time-varying properties and nonlinearities of gears and bearings were introduced. Gao and Zhang [3] investigated the gear-bearing dynamic interactions using a dynamic model of a rotor-bearing system with confluence transmission. Theodossiades and Natsiavas [4] studied the dynamic response of the gear-rotor coupled system under the action of oil film force and meshing force and not only investigated the oil film stability but also analyzed the amplitude-frequency response. Based on nonlinear theory, Wan and Chang [5] carried out a systematic analysis of the dynamic behaviors of a gear-rotor-bearing with strongly nonlinear.

Some scholars have thrown more lights to study the influence of backlash, time-varying meshing stiffness, and manufacturing error on the dynamic characteristics of planetary gear train. Based on elastodynamics, Guo and Parker [6] established a pure torsional dynamic model of the planetary gear train and analyzed the natural frequency and parametric sensitivity. Similarly, Zhang et al. [7] analyzed the characteristics of natural frequencies and mode shapes of an encased differential gear train. Wu et al. [8] studied the influence of backlash on the nonlinear characteristics of compound planetary gear set by analyzing the change of backlash with gear wear. Zhu et al. [9] explored the influence of multibacklash on bilateral shock of encased differential planetary gear train. Lin and Parker [10] used a multiscale method to investigate the influence of meshing stiffness waves on the stability of the planetary gear train, and they derived the analytical formula of the relationship between meshing stiffness variation and system dynamic stability. Al-Shyyab et al. [11] constructed a torsional dynamics model of a discrete two-stage planetary transmission system, and they studied the frequency response of the system under stiffness excitation. Considering time-varying meshing stiffness, Xiang et al. [12] developed a torsional nonlinear dynamic model of multistage planetary gear trains and studied the effects of bifurcation parameters such as excitation frequency, backlash, and damping.

In addition, Iglesias et al. [13] investigated the effects of eccentricity and planet pin positioning errors on the quasi-static behavior of planetary gear train for different configurations of support parameters. In terms of multiple errors (e.g., eccentricity error, base pitch error, and assembly error), Mo et al. [14] proposed an improved mathematical model of the loading sharing coefficient for compound planetary gear train, which was verified by experiments. Using a lumped parameter method, Zhai et al. [15] developed the bending-torsional-pendular coupled vibration model of the wind turbine gearbox transmission system and studied the frequency response of carrier assembly errors (e.g., carrier horizontal assembly error, carrier axis assembly error, and carrier spatial assembly error) to the dynamic meshing force and dynamic transmission error.

In most of the abovementioned studies, the planet bearing assumes a fixed stiffness spring and the bearing force is assumed to be linear with displacement. However, the asymmetry and interaction of oil film stiffness and damping of planet bearing is neglected. To fill this gap, we use four stiffnesses and four damping coefficients to explore the dynamic characteristics of encased differential gear train with journal bearing.

In this study, the marine encased differential gear train with journal bearing is taken as the research object. First, the lumped parameter method is utilized to establish a dynamic model of the encased differential gear train considering time-varying meshing stiffness and comprehensive transmission errors. Second, the asymmetry and interaction of the oil film stiffness and damping of journal bearing is employed to the dynamic model, and the gears and carrier are treated according to the concentrated mass. Third, the time-varying meshing stiffness of herringbone gears is calculated based on the time-varying total contact line length [16]. Fourth, the dynamic equations of coupling journal bearings are constructed by Newton’s second law. The dynamic response of encased differential gear train with journal bearing are solved by the numerical algorithm of Fourier series. Finally, the effects of parameters of planet bearing on the meshing forces are explored in detail.

2. Dynamic Model of Compound Planetary Gear Train

The encased differential gear train consisting of a single-degree-of-freedom encased planetary gear train (encased stage) and a two-degree-of-freedom differential planetary gear train (differential stage) is shown in Figure 1. In the differential stage, No. 1, No. 2, No. 3, No. 4, No. 5, No. 6, and No. 7, respectively, represent the floating ring gear Z_f1, the intermediate floating member , the composting ring gear Z_r1, the planet Z_pi (i = 1, 2, …, N, where N is the number of planets), the sun gear Z_s1, the carrier H, and planet bearing. In the encased stage, No. 8, No. 9, No. 10, No. 11, No. 12, and No. 13, respectively, represent the floating ring gear Z_f2, the intermediate floating member, the composting ring gear Z_r2, the planet Z_mj (j = 1, 2, …, M, where M is the number of planets), and the sun gear Z_s2, and planet bearing. No. 14 and No. 15 represent journal bearings at input and output shafts, respectively.

Herringbone gears are employed in the sun gears Z_s1/Z_s2 (i.e., No. 5/No. 12) and planet Z_pi/Z_m (i.e., No. 4/No. 11). The composting ring gear Z_r1/Z_r2 (i.e., No. 3/No. 10) is composed of internal and external helical gears on the same gear tooth germ. The intermediate floating member (i.e., No. 2/No. 9) is composed of internal helical and external spur gears on the same gear tooth germ. The internal helical gear of Z_r1/Z_r2 meshes with the unilateral helical gear of planet Z_pi/Z_mj, and the external helical gear of Z_r1/Z_r2 meshes with the internal helical gear of . The external spur gear of meshes with the internal spur gear of Z_f1/Z_f2 (i.e., No. 1/No. 8).

Figure 2 shows the dynamic model of the encased differential gear train. The rotational coordinate system based on the rotation angular velocity of carrier H is applied to the differential stage. The fixed coordinate system is used for the encased stage. The degree-of-freedom of the encased differential gear train is 19 + 3(N + M). Displacement parameter X is defined bywhere x_s1, x_pi, x_r1, x_s2, x_mj, and x_r2 are torsional line displacement parameters along base circle radius of Z_s1, Z_pi, Z_r1, Z_s2, Z_mj, and Z_r2, respectively. x_g1, x_f1, x_g2, and x_f2 are torsional line displacement parameters along the pitch circle radius of Z_f1, , Z_f2, and , respectively. x_H, H_H, and are torsional, lateral, and longitudinal displacements of carrier H, respectively. H_s1, H_pi, and H_r1 are lateral center displacements of Z_s1, Z_pi, and Z_r1, respectively, in their rotational coordinates. , , and are longitudinal center displacements of Z_s1, Z_pi, and Z_r1, respectively, in their rotational coordinates. H_s2, H_mj, and H_r2 are lateral center displacements of Z_s2, Z_mj, and Z_r2, respectively, in fixed coordinate. , , and are longitudinal center displacements of Z_s2, Z_mj, and Z_r2, respectively, in fixed coordinate.

2.1. Model for Calculation of Journal Bearing Stiffness and Damping

The dynamic model of the journal bearing is shown in Figure 3. Assuming that displacement and velocity remain small disturbances in the vicinity of the static position O₀ (x₀, y₀) [1], the first-order expansion of dynamic bearing forces (i.e., F_x and F_y) is defined bywhere is the partial derivative at static position O₀ (x₀, y₀).

Here,where F_x0 and F_y0 are static bearing forces in x and y directions, respectively. ΔF_x and ΔF_y are the increments of the oil film force. ξ and η are the increments of oil-film thickness in x and y directions, respectively. k_ij and d_ij (i, j = x, y) are the stiffness and damping coefficients of journal bearing, which are obtained bywhere B and d are the width and diameter of the journal bearing, μ is the oil viscosity, ε is the eccentricity ratio, ψ is the clearance-to-radius ratio, and K_ij and D_ij (i, j = x, y) are the corresponding dimensionless stiffness and damping coefficient of journal bearing.

2.2. Model for Calculation of Time-Varying Meshing Stiffness

The planets are evenly distributed among the sun gear in the planetary gear train. There are varying mesh phasing factors in meshing pairs (i.e., sun-planet and ring-planet) because of the influence of the number of teeth. The mesh phasing factor affects the phase of the time-varying meshing stiffness [17]. Therefore, the mesh phasing factor is incorporated into the encased differential gear train. Following Parker and Lin [18], the mesh phasing factor is defined bywhere γ_sm and γ_rm are the mesh phasing factor of sun-planet and ring-planet, respectively, and Z_s and Z_r are the teeth number of the sun and ring, respectively.

Maatar and Velex [16] proposed the time-varying meshing stiffness of helical gear pairs based on the time-varying total contact line length. Following Maatar and Velex [16], the time-varying meshing stiffness model of the helical gear is applied to the herringbone gear by a parallel method in this study. The time-varying meshing stiffness model of the herringbone gear is constructed as follows:where k₀ is the average value of the time-varying meshing stiffness, is dimensionless time, = t/T_m, t and T_m are meshing time and period, and L() is the instantaneous total contact length of gear pair, which is obtained bywhere γ is the mesh phasing factor, ε_α is the end-face contact ratio of the herringbone gear, β_b is the helical angle of the base circle of the herringbone gear, B is the unilateral tooth width of the herringbone gear, A_k and B_k are the kth-order harmonic amplitude of the time-varying meshing stiffness, S represents the order of the Fourier series, and the series is truncated at S = 5 in this article.

The parameters A_k and B_k are calculated bywhere ε_β is axial contact ratio of the herringbone gear.

2.3. The Equivalent Displacement and Meshing Forces

The center displacement of each gear is projected into the meshing line direction. We ignored the change of the meshing angle caused by the movement of each gear center. Figure 4 shows the positional relationship sun gear, planet, and composting ring gear in the differential stage.

The equivalent displacement of the ith planet-composting ring and sun-planet along meshing line direction can be calculated bywhere e_rpi and e_spi are the equivalent error of the ith planet-composting ring and sun-planet along meshing line direction.

According to the equivalent displacement calculation method of the differential stage, the equivalent displacement of the jth sun-planet and composting ring-planet along meshing line direction can be calculated by

The planet is supported by planet bearing in the encased differential gear train, and thus the compression deformation between carrier and planet bearing can be obtained bywhere δ_Hcpi is the compression deformation of planet bearing along the lateral direction and is the compression deformation along the longitudinal direction.

Elastic and damping meshing forces in the differential and encased stages can be calculated bywhere is the first derivative of equivalent displacement. C_i is the meshing damping factor, which can be calculated by [19]where ζ_i denotes the constant damping ratios of the gear pair, ζ_i = 0.07; k_0,i represents the average value of the meshing stiffness in the gear pair, and m_pi and are the masses of the driving and driven gears in the gear pair.

2.4. Differential Equations of the Compound Planetary Gear Trains

According to Figure 2 of the dynamic model of the encased differential gear train, differential equations of 19 + 3 (N + M) degree-of-freedom are constructed for the encased differential gear train by the lumped parameter method. Differential equations of the differential stage can be deduced using Newton’s second law as follows.(1)The sun gear Z_s1:(2)The ith planet gear Z_pi: where F_Hcpi(t) is the oil film force of the ith planet bearing in the lateral direction, is the oil film force of the ith planet bearing in the longitudinal direction, F_Hcpi(t) and are calculated by equation (3), and F_pi is the centrifugal force of the ith planet Z_pi.(3)The composting ring gear Z_r1:(4)The intermediate floating member and floating ring Z_f1:

Differential equations of the encased stage can be deduced using Newton’s second law as follows:(1)The sun gear Z_s2:(2)The jth planet gear Z_mj: where F_Hmj(t) is the oil film force of the jth planet bearing in the lateral direction and is the oil film force of the jth planet bearing in the longitudinal direction.(3)The composting ring gear Z_r2:(4)The intermediate floating member and floating ring Z_f2:

The differential equation of carrier H can be deduced by Newton’s law:where is the oil film force of journal bearing in the lateral direction and is the oil film force of journal bearing in the longitudinal direction.

3. Numerical Studies and Analysis

The dynamics simulation is performed with a constant power of 1000 kW. Different rotational speeds are applied to the differential stage sun gear. Table 1 lists the parameters of the encased differential gear train. The system response is solved by the numerical calculation method of the Fourier series [20]. The eccentricity ratio of the journal bearing is taken from 0.01 to 0.91. The clearance-to-radius ratio ranges from 0.1‰ to 2.5‰. The oil viscosity is 0.04 N·s/m².

3.1. Comparative Analysis of Spring Bearing and Journal Bearing

Before performing planet bearing parameter analysis, we calculate the dynamic deviation of the meshing force to investigate whether the encased differential gear train with journal bearing is more stable than the encased differential gear train with spring (i.e., planet bearings are replaced by fixed stiffness springs). The dynamic model of the encased differential gear train with spring is constructed by equations (14)–(22), and the stiffness of spring is 6 × 10⁶ N/m. According to the stiffness and damping coefficient of the journal bearing in Section 2.1, we establish the dynamic model of the encased differential planetary gear train with journal bearing. The dynamic deviation of meshing force (i.e., the degree of dynamic meshing force deviates from the theoretical static meshing force) is defined as follows [21]:where S_e and S_i represent the dynamic deviation of external and internal meshing forces, respectively, N is the number of planets, Q is the sampling times of the dynamic meshing force, and are external and internal instantaneous meshing force, respectively, and F_s is the theoretical static meshing force.

Figure 5(a) shows that, in the differential stage, the dynamic deviation curves of the external meshing force of the bearing model and the spring model are basically the same at a low rotational speed. However, the dynamic deviation curve of the external meshing force of the spring model has a peak when the rotational speed is 4800 r/min. It is worth noting that the dynamic deviation curve of the internal meshing force is approximately the same as that of the external meshing force (see Figures 5(a) and 5(b)). Figures 5(c) and 5(d) detail that, in the encased stage, the dynamic deviation curves of the meshing forces of the bearing model and the spring model are substantially the same. These findings indicate that at high rotational speeds, the oil film force of journal bearing can curb the vibration of the encased differential gear train. Therefore, we investigate the influence of the parameters of planet bearings on dynamic meshing forces in the next step.

(a)

(b)

(c)

(d)

3.2. Influence of the Differential Planet Bearing Parameters on Meshing Forces

After modeling differential equations of the encased differential gear train with journal bearing, the dynamic meshing force of differential equations can be calculated by equation (12). Besides, we use the root-mean-square to describe dynamic meshing forces.

3.2.1. Clearance-to-Radius Ratio

To investigate the effects of the differential planet bearing clearance-to-radius ratios on meshing forces, we set the clearance-to-radius ratio as 0.1‰, 0.5‰, 1‰, 1.5‰, 2‰, and 2.5‰, respectively (see Figure 6). The amplitude-frequency response curves of the meshing forces within the rotation speed range of 500–6000 r/min are calculated.

(a)

(b)

(c)

(d)

Figures 6(a) and 6(b) report that the amplitude-frequency response curves of meshing forces (i.e., external and internal) in the differential stage overlap at low rotational speed and diverge at a high rotational speed. This finding indicates that the impact of the clearance-to-radius ratio of the differential planet bearing on the meshing force is small when the rotational speed is low; the impact of clearance-to-radius ratio on the meshing force is obvious when the rotational speed is high. Figures 6(c) and 6(d) show that the amplitude-frequency response curves of meshing forces in the encased stage tend to diverge at low rotational speed and tend to overlap at a high rotational speed. Therefore, when the rotational speed in the encased planetary gear train is low, the clearance-to-radius ratio of the differential planet bearing should be reduced to diminish its influence on the meshing force to ensure the stability and reliability of the system.

3.2.2. Eccentricity Ratio

To investigate the influence of the eccentricity ratio of the differential planet bearing on meshing forces, the eccentricity ratios amount on the planet bearing are taken as 0.01, 0.19, 0.37, 0.55, 0.73, and 0.91, respectively. We calculate the amplitude-frequency response curves of meshing forces within the rotation speed range of 500–6000 r/min, as shown in Figure 7.

(a)

(b)

(c)

(d)

It can be seen from Figure 7(a) that, for different eccentricity ratios of the differential planet bearing, amplitude-frequency response curves are basically consistent. This finding indicates that the eccentricity ratio of the differential planet bearing has little effect on the external meshing force in the differential planetary gear train. Figure 7(b) reveals that amplitude-frequency response curves tend to diverge when the rotational speed is between 2000 r/min and 5000 r/min. This result indicates that when the rotational speed is between 2000 r/min and 5000 r/min, the eccentricity ratio of the differential planet bearing has a significant influence on the internal meshing force in the differential stage. Amplitude-frequency response curves tend to diverge at low rotational speed and tend to overlap at high rotational speed (see Figures 7(c) and 7(d)), suggesting that the impact of eccentricity ratio of the differential planet bearing on the meshing forces in the encased stage is obvious when the rotational speed is low.

3.3. Influence of the Encased Planet Bearing Parameters on Meshing Forces

3.3.1. Clearance-to-Radius Ratio

In this section, the impact of clearance-to-radius ratios of the encased planet bearing on meshing forces is explored. Similar to the differential planet bearing, we set the clearance-to-radius ratio of the encased planet bearing as 0.1‰, 0.5‰, 1‰, 1.5‰, 2‰, and 2.5‰, respectively, as shown in Figure 8.

(a)

(b)

(c)

(d)

Figures 8(a) and 8(b) uncover that the amplitude-frequency response curves of meshing forces (i.e., external and internal) in the differential stage are substantially uniform for different clearance-to-radius ratios of the encased planet bearing. Figures 8(c) and 8(d) show that the amplitude-frequency response curves of meshing forces in the encased stage tend to overlap at low rotational speed and tend to diverge at a high rotational speed. It is worth noting that the amplitude-frequency response curves of meshing forces in the encased stage have a peak when the rotational speed is between 1500 r/min and 2000 r/min. These findings indicate that when the rotational speed is between 1500 r/min and 2000 r/min, the clearance-to-radius ratio of the encased planet bearing has an obvious impact on the meshing forces in the encased stage, especially 1‰ and 0.5‰ clearance-to-radius ratios.

3.3.2. Eccentricity Ratio

Using the same eccentricity parameters as in Section 3.2.2, the impact of the eccentricity ratio of the encased planet bearing on dynamic meshing forces is investigated, as shown in Figure 9.

(a)

(b)

(c)

(d)

Figures 9(a) and 9(b) show that the corresponding amplitude-frequency response curves are the same regardless of which eccentricity ratio of the encased planet bearing is incorporated into our model. Similar to the clearance-to-radius ratio of the differential planet bearing, the eccentricity ratio of the encased planet bearing has a significant impact on the meshing forces in the encased stage when the rotational speed is between 1500 r/min and 2000 r/min (see Figures 9(c) and 9(d)). Besides, the eccentricity ratio of the encased planet bearing has more influence on the internal meshing force than on the external meshing force. Compared with Section 3.2.2, it can be found that the influence of the eccentricity ratio of the encased planet bearing on the meshing force of the encased stage is more significant than that of the differential stage.

4. Conclusions

Considering the factors of time-varying meshing stiffness and comprehensive transmission error, the dynamic model of encased differential gear train with journal bearing is established. The asymmetry and interaction of the oil film stiffness and damping of the planet bearings are employed in this dynamic model. The effects of planet bearing parameters on the meshing forces are explored, and the main conclusions are drawn as follows.

When the rotational speed is low, the stability of the encased differential gear train with journal bearing is basically the same as that of the encased differential gear train with spring. However, when the rotational speed is high, the encased differential gear train with journal bearing is more stable than the encased differential gear train with spring.

The clearance-to-radius and eccentricity ratio of the differential planet bearings affect the meshing forces of both the differential stage and encased stage. When the rotational speed is low, the influence of the clearance ratio and eccentricity ratio of the differential planet bearings on the meshing forces of the differential stage is less than that of the encased stage. However, this phenomenon is the opposite when the rotational speed is high.

The clearance-to-radius and eccentricity ratio of the encased planet bearing obviously affect the forces meshing of the encased stage, while they slightly affect the meshing forces of the differential stage. When the rotational speed is between 1400 r/min and 2000 r/min, the clearance-to-radius and eccentricity ratio of the encased planet bearing have a significant impact on the meshing forces of the encased stage.

Nomenclature

T_D/T_L:	Input/output torque
N/M:	Teeth number of planets of the differential/encased stage
Z_s1/Z_s2:	Sun gear of the differential/encased stage
Z_pi /Z_mj:	The ith/jth planet
Z_r1/Z_r2:	Composting ring gear of the differential/encased stage
Z_f1/Z_f2:	Floating ring gear of the differential/encased stage
:	Intermediate floating member of the differential/encased stage
Z_s/Z_r:	Teeth number of the sun/ring
T_m/t:	Meshing period/time
r_s1b/r_s2b:	Base circle radius of Z_s1/Z_s2
r_f1b:	Pitch circle radius of Z_f1
r_c:	Rotation radius of planet
k₀:	Average meshing stiffness
α_n/β:	Pressure/helical angle of gear
ε_α /ε_β:	End-face/axial contact ratio
β_b:	Helical angle of the base circle
ψ_i /ψ_j:	Phase angle of Z_pi/Z_mj: ψ_i = 2π(i − 1)/N, ψ_i = 2π(j − 1)/M
α_rp:	Meshing angle of Z_s1 − Z_pi
α_sp:	Meshing angle of Z_r1 − Z_pi
α_sm:	Meshing angle of Z_s2 − Z_mj
α_rm:	Meshing angle of Z_r2 − Z_mj
e_spi:	Equivalent error of Z_r1 − Z_pi
e_rpi:	Equivalent error of Z_r1 − Z_pi
e_smj:	Equivalent error of Z_s2 − Z_mj
e_rmj:	Equivalent error of Z_r2 − Z_mj
K_s1/K_s2:	Supporting stiffness of Z_s1/Z_s2
K_r1/K_r2:	Supporting stiffness of Z_r1/Z_r2
K^H_ξη/D^H_ξη:	Stiffness/damping of carrier bearing (ξ, η = X, Y)
K^p_ξη/D^p_ξη:	Stiffness/damping of the ith planet bearing (ξ, η = H, )
K^m_ξη/D^m_ξη:	Stiffness/damping of the jth planet bearing (ξ, η = H, )
K_f1s2:	Connection torsion stiffness of Z_f1 − Z_s2
K_f2H:	Connection torsion stiffness of Z_f2 − H
:	Contact tangential stiffness of Z_f1 −
K_f1q:	Contact tangential stiffness of − Z_r1
:	Contact tangential stiffness of Z_f2 −
K_f2q:	Contact tangential stiffness of − Z_r2
K_rpi:	Time-varying meshing stiffness of Z_r1 − Z_pi
K_spi:	Time-varying meshing stiffness of Z_s1 − Z_pi
K_rmj:	Time-varying meshing stiffness of Z_r2 − Z_mj
K_smj:	Time-varying meshing stiffness of Z_s2 − Z_mj
D_rp:	Meshing damping of Z_r1 − Z_pi
D_sp:	Meshing damping of Z_s1 − Z_pi
D_rm:	Meshing damping of Z_r2 − Z_mj
D_sm:	Meshing damping of Z_s2 − Z_mj
m_s1/M_s1:	Equivalent/actual mass of Z_s1
m_p/M_p:	Equivalent/actual mass of Z_pi
m_r1/M_r1:	Equivalent/actual mass of Z_r1
m_g1/m_f1:	Equivalent mass of /Z_f1
m_s2/M_s2:	Equivalent/actual mass of Z_s2
m_m/M_m:	Equivalent/actual mass of Z_mj
m_r2/M_r2:	Equivalent/actual mass of Z_r2
/m_f2:	Equivalent mass of /Z_f2
m_c/M_c:	Equivalent/actual mass of H.

Data Availability

The data used to support the findings of this study are available from the corresponding author upon request.

Conflicts of Interest

The authors declare that there are no conflicts of interest regarding the publication of this paper.

Acknowledgments

This work was supported by the National Key R&D Program of China (no. 2018YFB2001300) and National Natural Science Foundation of China (no. 51775265).

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Copyright © 2020 Jie Yang et al. This is an open access article distributed under the Creative Commons Attribution License, which permits unrestricted use, distribution, and reproduction in any medium, provided the original work is properly cited.

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