# Dynamic Model and Vibration Characteristics of Planar 3-RRR Parallel Manipulator with Flexible Intermediate Links considering Exact Boundary Conditions.

1. IntroductionCompared with the serial manipulator, the parallel manipulator has the advantages of high speed, high acceleration, high load capacity, low energy consumption, no-accumulation error, and high precision, which is widely used in aerospace, precision optical instruments, high-precision real-time measuring instruments, fast precision machine tools, and other fields [1]. Simultaneously, FPMs have attracted great social concerns and have been applied extensively. However, owning to the inertia force, dynamic load carrying capacity, and other factors, flexible intermediate links are prone to elastic deformation, which results in the decrease of the overall dynamic performance of the manipulator and influences the normal working of the FPM under the high speed with load condition. Elastic vibration has a greater impact on the accuracy and quality of the operation in the system [2, 3], for example, the elastic vibration of pick-and-place parallel manipulator in food packaging, directly affecting the quality of food [4]; the vibration of operating mechanism at the end of picking manipulator, leading to instability in grasping and damage to strawberry, tomatoes, and other soft appearance fruits [5, 6]. Therefore, the study of vibration characteristics of the FPM has important significance.

In order to further study the vibration problem of the planar 3-RRR FPM with flexible intermediate links, the dynamic model needs to be established which can accurately reflect the rigid-flexible coupling characteristics of the system. Furthermore, the vibration characteristics and the influences should be studied between the rigid body and the flexible body based on the model. In the existing literatures, the dynamic modeling method of the FPM is mainly from the energy point of view to obtain the partial differential equation. Then an approximation finite-dimensional ordinary differential equation is obtained by discretizing the complex continuous system model through the finite element method (FEM) [7, 8] and the AMM [9, 10]. Yu and Hong [11] described dynamic modeling, modal selection and modal synthesis, and dynamic stiffening of flexible multibody systems. Yu et al. [12] presented a dynamic model of the 3-RRR FPM and verified the correctness of the model through experiments. Zhang et al. [13, 14] established the dynamic model of the 3-RRR FPM using the finite element method and Lagrange equation and analyzed the influence of temperature and other factors on the elastic deformation of each flexible link. Zhang et al. [15] established the dynamic model of the 3-RRR FPM based on the energy method and illustrated the influence of the joint gap on the model. Fattah et al. [16] studied the dynamics of a 3-DOF parallel manipulator. Based on the finite element method and the Euler-Lagrange equation, the dynamic equations of the system were established. In order to emphasize the influence of system flexibility, the dynamics simulation experiment of rigid-flexible system was carried out. In spite of the high precision of the above models, the dynamic model described in the past literature has too many dynamic parameters, which makes the model difficult to solve and is disadvantageous to the design of subsequent controllers. In order to meet the requirements of the model premise, as far as possible to make the model simplification, low-level, easy to solve, and controller design, Mostafavi Yazdi and Irani [17] described the basic principle and modeling process of the AMM in detail and investigated the dynamic equations of the beam model with two teeth which were established by the AMM. Compared with the general beam model, the elastic vibration of the tooth beam is smaller. Chen [18] established a linear dynamic model of a multiflexible linkage manipulator by Lagrange equation and AMM. During the dynamic modeling of planar FPM with flexible intermediate links, Zhang et al. [19, 20] elaborated the dynamic model of FPM with flexible intermediate links which was established using the boundary conditions of pinned-pinned at both ends of the flexible intermediate links based on AMM and the Lagrange equation. However, the experiment in [21, 22] proved that, in the motion control, because of the elastic deformation of the flexible link, the dynamic platform produced violent vibration. It can not explain this phenomenon well using pinned-pinned boundary conditions vibration mode to discretize the flexible deformation.

Different from current literatures, in this paper, based on the extended Hamilton principle and AMM, with the pinned-free boundary condition for the flexible intermediate link, the dynamic model of the 3-RRR FPM with flexible intermediate links is established with considering the effect of rotor and the concentrated moment of inertia at both ends of link and the rigid-flexible coupling. The dynamic model established cannot only satisfy the model precision but also solve the dynamic model easily. The dynamic response and the natural frequency of the flexible intermediate link are obtained by solving the dynamic equation. Based on the model, the influence of the coupling force and inertial force on the system and the driving torque of the motor are analyzed. Finally, the correctness of the model is verified by modal experiment. This provides a theoretical basis for the optimal design of the system structure and shock absorbers and the selection of motors.

The structure of the paper is as follows. The second chapter introduces the system overview and dynamic modeling of the planar 3-RRR FPM. The numerical simulations and results discussions are shown in third chapter. The forth chapter is the experimental verification section. Finally, the paper is concluded with a brief summary.

2. The System Overview and Dynamic Modeling of the Planar 3-RRR FPM

The system structure and the coordinate system of the planar 3-RRR FPM are shown in Figure 1. X[A.sub.1]Y is the global coordinate system. xPy is the moving coordinate system which follows the moving platform. The system is composed of the moving platform [C.sub.1][C.sub.2][C.sub.3] and the fixed base [A.sub.1][A.sub.2][A.sub.3] as well as three identical branches [A.sub.1][B.sub.1][C.sub.1], [A.sub.2][B.sub.2][C.sub.2], and [A.sub.3][B.sub.3][C.sub.3]. As Figure 1 shows, [A.sub.1], [A.sub.2], and [A.sub.3] are the three vertices of the regular triangle whose side length is 500 mm, where the active revolute joints are set. The points of [B.sub.1], [C.sub.1], [B.sub.2], [C.sub.2], [B.sub.3], and [C.sub.3] are the passive revolute joints, where [A.sub.1][B.sub.1] = [A.sub.2][B.sub.2] = [A.sub.3][B.sub.3] = [B.sub.1][C.sub.1] = [B.sub.2][C.sub.2] = [B.sub.3][C.sub.3] = Lt = 210 mm. The radius of the circle of joints in moving platform is R = 68 mm. The 3-DOF planar motion can be achieved by using the three driving motors in the three active joints.

In the actual structure, the cross-sectional area of the drive rod is larger to ensure its rigidity, while the cross-sectional area of the intermediate link is smaller to reduce its mass. Therefore, in this paper, only the flexible intermediate links of the flexible planar 3-RRR parallel robots are considered as the flexible part; others are the rigid part. The vibration of the mechanism is mainly caused by the motor drive, the inertial force, and the payload of the moving platform.

2.1. Dynamic Modeling of Flexible Intermediate Link. The schematic diagram of the ith branch and moving platform are shown in Figure 2. The transverse deformation is smaller compared with the length of the flexible intermediate link, so the equation can be modeled linearly according to the linear elastic deformation. The flexible intermediate link is considered as a pinned-free Euler-Bernoulli beam. The radial and lateral stiffness is ignored, and the uncertainty of modeling and other parameters is regarded as a kind of parameter perturbation. Since the flexible intermediate link moves in the horizontal plane, the effect of gravity is not considered. The kinetic energy mainly includes the rotational kinetic energy of the motor rotor and the rotational kinetic energy of the joint [A.sub.i], the translational kinetic energy of driving rod, the concentrated translational kinetic energy of the joint [B.sub.i] and its own rotational kinetic energy, and the translational kinetic energy of the intermediate link, where the rotational kinetic energy of joints [A.sub.i] and [B.sub.i] is mainly produced by its internal bearing. It can be expressed as

[mathematical expression not reproducible], (1)

where [mathematical expression not reproducible] is the rotational kinetic energy of the ith drive joint [A.sub.i] and the motor rotor; [mathematical expression not reproducible] is the kinetic energy of the ith driving rod; [mathematical expression not reproducible] is the kinetic energy of the joint [mathematical expression not reproducible] is the kinetic energy of the ith flexible intermediate link; [w.sub.i]([x.sub.i], t) is the transverse elastic displacement of x points on flexible intermediate link; [mathematical expression not reproducible] is the unit length mass of the ith flexible intermediate link; [mathematical expression not reproducible] is the mass of the joint [B.sub.i]; [mathematical expression not reproducible] is the rotational inertia of the driving joint [A.sub.i] and the motor rotor; [mathematical expression not reproducible] is the rotational inertia of joint [mathematical expression not reproducible] is the vector coordinates of the ith drive rod; [mathematical expression not reproducible] is the vector coordinates of the ith flexible intermediate link; ([??]) and (w') are the differential for the time and displacement, respectively.

The potential energy of the ith branch of the system is expressed as

[mathematical expression not reproducible], (2)

where [E.sub.i] is the elastic modulus and I([x.sub.i]) is the moment of inertia of section of flexible intermediate link.

The virtual work of the ith branch of the system can be expressed as

[mathematical expression not reproducible], (3)

where [[bar.f].sub.ixy] = [[f.sub.ix] [f.sub.iy]] is the constraint force between the joint [C.sub.i] and the end of the flexible intermediate link. [mathematical expression not reproducible] is the drive torque of the ith servomotor. [mathematical expression not reproducible], is the virtual displacement vector at the end of the ith flexible intermediate link. [delta][[alpha].sub.i] is the virtual angle displacement of the ith servomotor.

Based on the extend Hamilton principle [23], the boundary conditions and the kinetic differential equation can be derived as follows:

[mathematical expression not reproducible], (4)

where [[bar.[eta]].sub.i] = [[[[alpha].sub.i] [[beta].sub.i] [w.sub.i]].sup.T] is the generalized variable of the ith branch.

According to the extended Hamilton principle, the total energy of the ith branch is varied to the generalized variable. Considering the interchangeability between variational and differential, the similar items are combined after integrating the variational components by fractional integration over time t1 to t2. Since [mathematical expression not reproducible] can be assigned any value, three differential equations for generalized variables and four boundary conditions for flexible intermediate links are obtained. Since the flexible intermediate link is pinned to joint [B.sub.i], the deformation of the pinned joint is zero according to [24, 25]. This conclusion is used to simplify the differential equation.

The differential equation about [delta][[alpha].sub.i] is as follows:

[mathematical expression not reproducible]. (5)

The differential equation about [delta][[beta].sub.i] is as follows:

[mathematical expression not reproducible]. (6)

The differential equation about Swt is as follows:

[mathematical expression not reproducible]. (7)

The four nonhomogeneous boundary conditions of the flexible intermediate link are as follows:

[mathematical expression not reproducible]. (8)

In order to obtain the homogeneous boundary condition for flexible deformation discrete based on AMM, the Dirac function deformation is introduced according to [22].

[mathematical expression not reproducible]. (9)

Substituting (9) into (7) and (8),

[mathematical expression not reproducible], (10)

[mathematical expression not reproducible]. (11)

As can be seen from (11), the deflection and bending moment at the joint [B.sub.i] are zero, and the bending moments and shear forces at the joint [C.sub.i] are zero. Therefore, the pinned-free boundary conditions are satisfied for the flexible intermediate link.

2.2. Elastic Deformation Discretization of Flexible Intermediate Link. After the above analysis, we can find that the established equation is a highly nonlinear differential equation with rigid motion and elastic motion coupling, and the analytical solution is difficult. Therefore, it is considered to use the AMM to discretize the elastic deformation of the flexible link and then to solve the numerical solution for dynamic analysis. According to AMM, the deformation of the flexible intermediate link can be expressed as follows:

[mathematical expression not reproducible], (12)

where [q.sub.ij] (t) denotes the unknown generalized elastic variable of the ith flexible intermediate link. [[phi].sub.ij] ([x.sub.i]) is the mode function corresponding to the known boundary condition.

From the analysis of the previous section, the mode shape function with pinned-free boundary conditions of the flexible intermediate link is used to discrete elastic deformation. As can be seen from [24], the modal functions under the pinned-free boundary condition are shown as follows:

[mathematical expression not reproducible]. (13)

Equations (12) and (13) are substituted into (5), (6), and (7), respectively.

[mathematical expression not reproducible], (14)

[mathematical expression not reproducible], (15)

[mathematical expression not reproducible]. (16)

2.3. Dynamic Model of Moving Platform. The moving platform is considered to be a rigid body in the modeling process. The dynamic equation of the moving platform is as follows:

[mathematical expression not reproducible], (17)

where [mathematical expression not reproducible]is the quality of the moving platform. [J.sub.[phi]p] is the moment of inertia of the moving platform. ([x'.sub.ci], [y'.sub.ci]) is the coordinate of the joint Ct in the local coordinate system.

2.4. Rigid-Flexible Coupling Dynamics Model. Combining the dynamic equation of the moving platform with the kinetic equation of the branch, the rigid-flexible coupling ordinary differential equation of the 3-RRR FPM can be obtained as follows:

[mathematical expression not reproducible], (18)

where [mathematical expression not reproducible] is the generalized coordinate variable. [mathematical expression not reproducible] is the rigid body motion coordinate. [mathematical expression not reproducible] is the elastic coordinate of three flexible intermediate links. [bar.P] = [mathematical expression not reproducible] represents the driving torque of the three motors. [J.sub.f] is the binding matrix. The detailed form of the matrix is shown in Appendix.

[mathematical expression not reproducible] is the constraints of internal force of the joint [C.sub.i]. M is a positive definite symmetric mass matrix. C is the centrifugal force and Coriolis matrix. K is the stiffness matrix.

3. Numerical Simulation

The specific material and dimension parameters of the planar 3-RRR FPM are as follows: the material is aluminum alloy 7075. The elastic modulus of the material is [E.sub.i] = 7.1 x [10.sup.10] N/[m.sup.2]. The density is [[rho].sub.i] = 2.81 x [10.sup.3] kg/[m.sup.3]. The length, width and thick of the drive rod are 210 mm, 25 mm, and 10 mm, respectively. The length, width, and thick of the flexible intermediate link are 210 mm, 25 mm, and 2 mm, respectively. The moment of inertia of the motor rotor and drive joint is the [mathematical expression not reproducible]. The concentrated moment of inertia at the end of flexible intermediate link is [mathematical expression not reproducible]. The moment of inertia of section of flexible intermediate link is I([X.sub.i]) = 1.67 x [10.sup.-11] [m.sup.4].

In order to simulate the end of the operating conditions, a typical circular equation is given for its trajectory as follows:

[x.sub.p] = 0.31 - 0.06 cos (50[pi]t) (m), [y.sub.p] = 0.25 [square root of 3] + 0.06 sin (50[pi]t) (m). (19)

The numerical simulation results are as follows.

Figure 3 shows that the amplitude of the first-order end vibration response of the flexible intermediate link is larger. This vibration is sufficient to affect the stability and dynamic performance of the system. Therefore, with the flexible intermediate link 1 as an example, the second-order vibration response and frequency characteristics are further studied. The amplitude-frequency characteristics can be obtained through fast Fourier transform. The results are shown in Figures 4 and 5.

As shown in Figure 4, the fast Fourier transform of the first-order response curve shows that the frequency components are mainly 24.88 Hz, 49.75 Hz, and 104.5 Hz. Through the same treatment, the second-order frequency components are mainly 24.88 Hz, 49.75 Hz, and 288.6 Hz as shown in Figure 5. In order to further study the composition of frequency components, the inertial force and coupling force analysis are shown in Figure 6.

The mainly frequency of 24.88 Hz and 49.75 Hz caused by inertia force and coupling force can be seen from Figure 6, which also represents that the frequency 104.5 Hz in Figure 4 is natural frequency and the frequency 104.5 Hz in Figure 5 is second-order frequency of the flexible intermediate link. The driving torque of the motor can also be obtained through the dynamic equation, which provides the basis for the motor selection.

It can be seen from Figure 7 that the maximum driving torque of the motor does not exceed 20 N-m.

4. Modal Test Verification

In order to verify the correctness of the dynamic model established in this paper, the modal test bench is built as shown in Figure 8. The test bench is mainly composed of computer, DH5927N dynamic tester, hammer, piezoelectric acceleration sensor, charge adapter, and flexible 3-RRR FPM. A total of 11 test points were set up, among which the measuring points 1 and 11 were at the bearing, so no measurement was made.

During the course of the experiment, the three drive motors are locked in the initial position and the end moving platform is in the central position. The multipoint excitation and the pick-up one point test method is implemented. In order to achieve a more accurate result, the test is performed 5 times repeatedly, and then the results are averaged. The test data is collected and recorded by the DH5927N dynamic tester. The dynamic response is analyzed by PolyLscf method, and the results are shown in Figure 9.

The results show that the first-order frequency is mainly around 103.1 Hz and the damping ratio is 0.056. In addition the second-order vibration frequency is around 286.3 Hz and the damping ratio is 0.032. Compared with the frequency characteristics obtained through modal experiment and theoretical calculation, the first-order frequency 103.1 Hz and the second-order frequency 286.3 Hz obtained through modal test are basically consistent with the theoretical results 104.5 Hz and 288.6 Hz, which proves the correctness of the dynamic model established using the extended Hamilton principle and the AMM with the pinned-free boundary condition. Compared with the results obtained by other researchers [20], the model established in this paper has higher accuracy. The results' comparison is shown in Table 1.

The source of error between present work and others in the results is mainly in the selection of boundary conditions. This paper chooses the pinned-free boundary condition for the flexible intermediate link in the establishment of the mathematical model, while the boundary condition in the literature [20] is the pinned-pinned, and the joint gap caused by the machining and installation accuracy in the actual test bench is also part of the source of the error.

5. Conclusions

In this paper, based on the extended Hamilton principle and the AMM, the coupled dynamic model of planar 3-RRR FPM with high precision and less dynamic parameters is established with pinned-free boundary condition. This model takes into account the concentrated moment of inertia and rigid-flexible coupling effect on system dynamic. The first-order frequency 103.1Hz and the second-order frequency 286.3 Hz obtained through modal experiment are very close to the theoretical results 104.5 Hz and 288.6 Hz. The research indicates that the established dynamic model has a high accuracy. Based on the established dynamic model, it is found that the inertial force and the coupling force can cause the forced vibration, the vibration frequencies are 24.88 Hz and 49.75 Hz, and the driving torque of the motor does not exceed 20 N-m which can provide a basis for motor selection. The rigid-flexible coupling dynamics modeling method proposed in this paper is applicable to all kinds of FPM with flexible link. The model has high precision and high efficiency, which solves the problem of complexity of dynamics model and is of great significance to the controller design based on the dynamic model.

Appendix

[mathematical expression not reproducible]. (A.1)

Nomenclature [A.sub.i]: Active revolute joint [B.sub.i], [C.sub.i]: Passive revolute joint [L.sub.i]: Rod length R: Radius of the circle of joints in moving platform [[alpha].sub.i]: Angle between the driving link and the x-axis [[beta].sub.i]: Angle between the flexible intermediate link and the x-axis [x.sub.i], [y.sub.i]: Distance between a point and joint [A.sub.i] on driving link in the x, y direction [x.sub.ai], [y.sub.ai]: Distance between a point and joint [B.sub.i] on flexible intermediate link in the x, y direction [T.sub.i]: Total kinetic energy of the ith branch [mathematical expression Rotational kinetic energy of the ith not reproducible]: drive joint and the motor rotor [mathematical expression Kinetic energy of the ith driving rod not reproducible]: [mathematical expression Kinetic energy of the joint [B.sub.i] not reproducible]: [mathematical expression Kinetic energy of the ith flexible not reproducible]: intermediate link [w.sub.i]([x.sub.i], t): Transverse elastic displacement of x points on flexible intermediate link r: Assumed mode [rho]: Material density [mathematical expression Unit length mass of the ith flexible not reproducible]: intermediate link [mathematical expression Mass of the joint [B.sub.i] not reproducible]: [mathematical expression Rotational inertia of the driving joint not reproducible]: [A.sub.i] and the motor rotor [mathematical expression Rotational inertia of joint [B.sub.i] not reproducible]: [V.sub.i]: Vector coordinates of the ith drive rod [[??].sub.i]: Vector coordinates of the ith flexible intermediate link ([[alpha].sub.i], Differential for the time and [[beta].sub.i], [??]) displacement, respectively (w'): [V.sub.i]: Potential energy of the ith branch [E.sub.i]: Elastic modulus I([x.sub.i]): Moment of inertia of section of flexible intermediate link [delta][W.sub.i]: Virtual work of the ith branch [[bar.f].sub.ixy]: Constraint force between the joint [C.sub.i] and the end of the flexible intermediate link [mathematical expression Drive torque of the ith servomotor not reproducible]: [mathematical expression Virtual angle displacement not reproducible]: [[bar.[eta]].sub.i]: Generalized variable of the ith branch [q.sub.ij](t): Unknown generalized elastic variable of the ith flexible intermediate link [[phi].sub.ij] (x): Mode function corresponding to the known boundary condition [m.sub.p]: Quality of the moving platform [J.sub.[phi]p]: Moment of inertia of the moving platform ([x'.sub.ci], [y'.sub.ci]): Coordinate of the joint [C.sub.i] in the local coordinate system M: Positive definite symmetric mass matrix C: Centrifugal force and Coriolis matrix K: Stiffness matrix [x.sub.p][y.sub.p] Motion coordinate of moving platform [[phi].sub.p]: [bar.[eta]]: Generalized coordinate variable [bar.[alpha]], Rigid body motion coordinate [bar.[beta]], [[bar.X].sub.P]: [bar.q]: Elastic coordinate of three flexible intermediate links [bar.P]: Driving torque of the three motors [J.sub.f]: Binding matrix [bar.f]: Constraints of internal force of the joint [C.sub.i] i = 1,2,3: The 1,2,3 branch, respectively.

https://doi.org/10.1155/2017/1582547

Conflicts of Interest

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

Acknowledgments

This research work was supported by the National Natural Science Foundation of China (no. 51305444, no. 51307172, and no. U1610111), the Scientific and Technological Project of Jiangsu Province (BY201402806), the Project Funded by the Priority Academic Program Development of Jiangsu Higher Education Institutions (PAPD), and Six Talent Peaks Project in Jiangsu Province (ZBZZ-041).

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Lianchao Sheng, Wei Li, Yuqiao Wang, Mengbao Fan, and Xuefeng Yang

School of Mechatronic Engineering, China University of Mining and Technology, Xuzhou 221116, China

Correspondence should be addressed to Wei Li; cmeecumt512@yahoo.com

Received 11 January 2017; Revised 28 March 2017; Accepted 24 May 2017; Published 12 July 2017

Academic Editor: Tai Thai

Caption: FIGURE 1: The structure diagram of the planar 3-RRR FPM.

Caption: FIGURE 2: Schematic diagram of the ith branch and moving platform.

Caption: FIGURE 3: Vibration response curves of the end of the flexible intermediate links.

Caption: FIGURE 4: The first-order response and amplitude-frequency characteristics of the first flexible intermediate link.

Caption: FIGURE 5: The second-order response and amplitude-frequency characteristics of the first flexible intermediate link.

Caption: FIGURE 6: The response and amplitude-frequency characteristics of inertial force and coupling force.

Caption: FIGURE 7: Three motor drive torque.

Caption: FIGURE 8: Modal test bench.

Caption: FIGURE 9: Modal test results.

TABLE 1: The results comparison. Project The results of The results this article of others First-order simulation frequency 103.1 Hz 70.5Hz ([S.sub.1]) First-order experiment frequency 104.5 Hz 76.6 Hz ([E.sub.1]) Second-order simulation frequency 286.3 Hz 280.8 Hz ([S.sub.2]) Second-order experiment frequency 288.6 Hz 231.2Hz ([E.sub.2]) First-order relative error ([S.sub.1] - 1.36% 8.65% [E.sub.1])/[S.sub.1] x 100% Second-order relative error 0.8% 17.66% ([S.sub.2] - [E.sub.2])/[S.sub.2] x 100%

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Title Annotation: | Research Article |
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Author: | Sheng, Lianchao; Li, Wei; Wang, Yuqiao; Fan, Mengbao; Yang, Xuefeng |

Publication: | Shock and Vibration |

Article Type: | Report |

Date: | Jan 1, 2017 |

Words: | 5050 |

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