# Vibration Suppression Control of a Flexible Gantry Crane System with Varying Rope Length

Authors: Tung Lam Nguyen; Trong Hieu Do; Hong Quang Nguyen
Journal: Journal of Control Science and Engineering
 (2019)

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## Abstract

The paper presents a control approach to a flexible gantry crane system. From Hamilton’s extended principle the equations of motion that characterized coupled transverse-transverse motions with varying rope length of the gantry is obtained. The equations of motion consist of a system of ordinary and partial differential equations. Lyapunov’s direct method is used to derive the control located at the trolley end that can precisely position the gantry payload and minimize vibrations. The designed control is verified through extensive numerical simulations.


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## Body

## 1. Introduction

Gantry cranes are essential for load handling operation in various fields. Due to the flexibility in the gantry system structure, there exists a trade-off between the requirement of fast operations and minimizing payload vibration. Currently, solving the aforementioned constraint is an open and promising research area.Renowned for its simplicity in practical applications, input command shaping is one of the earliest attempts to crane control [1–6]. Maghsoudi et al. combine input shaping with particle swarm based optimization for a 3D gantry crane control problem in [7]. The improved method shows better performances in terms of vibration reduction with the presence of system friction and varying rope length. However, due to its open-loop structure, input shaping faces a serious difficulty in handling system with disturbances. Fulfilling this gap, Park et al. propose a feedback linearization for trolley and hoisting operations to guarantee asymptotic stability. Similarly, a partial feedback control is developed in [8]; the control is a linear combination of feedback linearization from actuated and unactuated dynamics. Subsequently, the closed-loop system is proven to be asymptotically stable. A novel motion-planning is designed based on minimum time control principle in combination with swing suppression control which is formulated in [9] for a class of high speed hoisting cranes; a remarkable contribution of the paper is robustness and uncertainty independent of the kinematic model. An analogous idea of using predefined trajectories is adopted in [10] where the author achieves the optimal trajectory for the gantry by employing radial basic function networks assisted by a particle swarm optimization scheme. In the quest of avoiding dependence on system parameters and system robustness, Tuan et al. use sliding mode as a control core in conjunction with other techniques such as model reference adaptive control [11] for crane systems. In addition, variations of sliding mode control can be found in [12] where super twisting based sliding mode controls are considered. Different from traditional gantry system structure with control attached to the trolley end, Schlott et al. [13] propose an actuated load structure for decoupling control purpose. A visual feedback scheme is developed by Lee at al. [14], visual information of a 3D crane is sent to an adaptive fuzzy sliding mode control, and as a result the close-loop system possesses robustness and model-free nature. Several approaches to the gantry system were also mentioned in [15–17].The above-mentioned works treat crane motion as pendulum-like motion where the crane cable is considered as a rigid body. Hence, the crane equations of motion consist of ordinary differential equations. In practice, the crane cable is flexible; this property leads to a requirement of a set of partial differential equations describing the crane motion. Joshi et al. [18] propose a control law based on Lyapunov stability for a flexible gantry. Similarly, looking at the gantry with flexible cable, D’Andréa-Novel et al. [19] design a feedback control that can stabilize the system exponentially. Considering the gantry with hoisting operation, Moustafe et al. [20] derive a boundary control for the system with varying rope length. With efforts to force payload vibration in a predefined range He et al. [21] formulate a control scheme for flexible gantry with a support of actuated payload and Nguyen et al. [22] develop control forces acting at the trolley end of a two-dimensional gantry.In the paper, a position control and vibration suppression of a 3D gantry crane with varying rope length are considered. The contribution of the research is the formulation of of 3D flexible gantry with coupling mechanism in transverse-transverse and transverse-longitudinal directions and the control designed for stabilizing the system. The system equations of motion are derived via Hamilton’s extended principle. Subsequently, control forces are constructed based on Lyapunov’s stability. Extensive simulations are presented to demonstrate the effectiveness of the proposed control.


## 2. Problem Formulation

Before deriving the gantry system mathematical model, the following is assumed:(1)
Cable axial deformation is very small in comparison with the cable length.(2)
The payload is considered as a point-mass.(3)
Friction in trolley motion is ignored.(4)
Environmental disturbances are neglected.(5)
Moving mass inX and Y directions are equal.(6)
The deflection angle of the cable from vertical axis is very small.(7)
Diameter to length ratio of the cable is very large.Assumption(1) implies that the axial deformation of the cable is ignored; however, transverse deformation is considered. Assumptions (2), (3), and (4) imply that the paper targets on small-size automated crane systems, where point-mass payload and zero disturbances assumptions are justified. Assumption (5) is placed to simplify the mathematical formulation process without loss of generality. Assumption (6) is generally accepted in practice. Assumption (7) suggests that string model is used.The crane system coordinate is depicted in Figure1, where x(t) and y(t) are the trolley positions in X and Y, respectively. A material point in Z direction is represented by z(t) and l(t) denotes the cable total length. The distance from a cable material point to the trolley in X and Y directions is n(t) and μ(t). The position vector of cable material point p is defined as(1)r→p=xt+nzt,ti→+yt+μzt,tj→+ztk→where i→ and k→ are unit vectors in X and Z directions, respectively. From (1), the velocity vector can de deduced as follows:(2)v→p=xtt+ntzt,t+zttnzzt,ti→+ytt+μtzt,t+zttμzzt,tj→+zttk→In similar fashion, the velocity vectors of the trolley and payload can be written as(3)v→mp=xtt+n¯tzt,t+lttn¯zzt,ti→+ytt+μ¯tzt,t+lttμ¯zzt,tj→+lttk→ and(4)v→mT=xtti→+yttj→ where n¯t=∂nl(t),t/∂t, n¯z=∂nl(t),t/∂z, μ¯t=∂μlt,t/∂t, μ¯z=∂μl(t),t/∂z.Figure 1
System coordinate.For the sake of clarity, from this point onward(•)t, (•)tt, (•)z, and (•)zz are used to denote ∂•/∂t, ∂•2/∂t2, ∂•/∂z, and ∂•2/∂z2, respectively, and the argument (t) is dropped where there is no confusion. The system coordinate depicted in Figure 1 suggests that the geometry boundary conditions for the crane system are(5)n0,t=nt0,t=μ0,t=μt0,t=0The total kinetic energy of the system induced by the cable, trolley, and payload motion is given by(6)KE=12ρ∫0ltxt+nt+ztnz2+yt+μt+ztμz2+zt2dz+12mTxt2+yt2+12mpxt+n¯t+ltn¯z2+yt+μ¯t+ltμ¯z2+lt2where ρ is the cable material density, mT is the trolley mass, and mP denotes the payload mass. The system potential energy is(7)PE=12∫0ltmpg+ρgl-znz2+μz2dz+12EA∫0lt12nz2+μz22dz-mpgl-∫0ltρgzdzwhere E is Young’s modulus and A is the cable cross section area. The first term represents potential energy caused by the rope tension, the second term is the strain energy, and the two last terms are generated by gravity of the cable and payload. The virtual work is(8)W=FXx+FYy+FLlThe virtual work in (8) is generated by force acting on the trolley and winch in X, Y, and Z directions. Applying the extended Hamilton principle(9)∫t1t2δKE-δPE+δWdt=0where δ is variation operation. Substituting (6), (7), and (8) into (9) and carefully integrating by parts results in the following equations of motion of the cable in X and Y directions(10)ρxtt+ntt+zttnz+zt2nzt+ztnzz=Tnzz+12EA3nz2nzz+nzzμz2+2nzμzμzz(11)ρytt+μtt+zttμz+zt2μzt+ztμzz=Tμzz+12EA3μz2μzz+μzznz2+2μznznzzwhere T=mpg+ρg(l-z). Governing equations of trolley motions in X and Y directions are given by(12)∫0ltρxtt+ntt+zttnz+zt2nzt+ztnzzdz+mTxtt+mpxtt+n¯tt+lttn¯z+lt2n¯zt+ltn¯zz=FX(13)∫0ltρytt+μtt+zttμz+zt2μzt+ztμzzdz+mTytt+mpytt+μ¯tt+lttμ¯z+lt2μ¯zt+ltμ¯zz=FYLowering and hoisting motions of the payload are represented by(14)∫0ltρxtt+ntt+zttnz+zt2nzt+ztnzznz+μzt+ztμzzyt+μt+ztμz+ztt+Tnznzz+μzμzz+12nz2+μz2nznzz+μzμzzdz+mpxtt+n¯tt+lttn¯z+lt2n¯zt+ltn¯zzn¯z+ytt+μ¯tt+lttμ¯z+lt2μ¯zt+ltμ¯zzμ¯z+ltt-12ρxt+n¯t+ltn¯z2+yt+μ¯t+ltμ¯z2+lt2+12mpgn¯z2+μ¯z2+12EA12n¯z2+μ¯z22=Fl¯where F¯l=Fl+mpg+2ρgl. The natural boundary conditions are(15)ρxt+n¯t+ltn¯zlt-mpgn¯z-12EAn¯z2+μ¯z2n¯z=mpxtt+n¯tt+lttn¯z+lt2n¯zt+ltn¯zz(16)ρyt+μ¯t+ltμ¯zlt-mpgμ¯z-12EAn¯z2+μ¯z2μ¯z=mpytt+μ¯tt+lttμ¯z+lt2μ¯zt+ltμ¯zzand the geometry boundary conditions given in (5). The system of equations describes the gantry dynamics including the cable deformation in X and Y directions with varying length. It is noted that, due to motion the cable flexibility, coupling mechanisms between transverse-transverse and transverse-longitudinal motions appear in the system dynamics. The coupling phenomenon causes a challenge in stabilizing the system. In addition, moving boundary at l(t) due to lowering and hoisting motions makes the control problem even worse. The 3D crane dynamic is considered in the paper different from models given in [20] where only one transverse direction is considered and in [22] where the rope length is unchanged. The main contribution of the paper is formulation and control design process of the 3D crane system with dynamical couplings.


## 3. Control Design

The control objective is to simultaneously drive the payload to desired position while keeping swing angle as small as possible. In order to archive the control objective, consider the following Lyapunov candidate function(17)Vt=12∫0ltρxt+nt+ztnz2+yt+μt+ztμz2+zt2+Tnz2+μz2+14EAnz2+μz22dz+12k1mTxt2+yt2+12mpxt+n¯t+ltn¯z2+yt+μ¯t+ltμ¯z2+lt2+12k2x-xd2+12k3y-yd2+12k4l-ld2.where ki,i=1,2,3,4 are strictly position constant and xd, yd, and ld are the desired position coordinates. The Lyapunov candidate function is radially unbounded and positive definite. It is also noted that the Lyapunov candidate function comprises the system kinetic, potential energy, and the error between current, and targeted positions. Differentiating (17) along the solutions of the equations of motion results in(18)V˙t=∫0ltρxt+nt+ztnzxtt+ntt+zttnz+zt2nzt+ztnzz+yt+μt+ztμzytt+μtt+zttμz+zt2μzt+ztμzz+ztztt+Tnznzzzt+nznzt+μzμzzzt+μzμzt+12EAnz2+μz2nznzzzt+nznzt+μzμzzzt+μzμztdz+12ρltxt+n¯t+ltn¯z2+yt+μ¯t+ltμ¯z2+lt2+12mpgltn¯z2+μ¯z2+18EAltn¯z2+μ¯z22+k1mTxtxtt+ytytt+mpxt+n¯t+ltn¯zßxtt+n¯tt+lttn¯z+lt2n¯zt+ltn¯zz+yt+μ-t+ltμ-ytt+μ-tt+lttμ-z+lt2μ-zt+ltμ-zz+ltltt+k2x-xdxt+k3y-ydyt+k4l-ldltApplying the equations of motion and boundary conditions, it can be shown that(19)V˙t=k1FXxt+k2x-xdxt+k1FYyt+k3y-ydyt+Fl¯lt+k4l-ldlt+∫0ltntTnzz+12EA3nz2nzz+nzzμz2+2nzμzμzzdz+∫0ltμtTμzz+12EA3μz2μzz+μzznz2+2μznznzzdz+12EA∫0ltnz2+μz2nznzt+μzμztdz+∫0ltTnznzt+μzμztdz+ρn¯txt+n¯t+ltn¯zlt-mpgn¯tn¯z-12EAn¯tn¯z2+μ¯z2n¯z+ρμ¯tyt+μ¯t+ltμ¯zlt-mpgμ¯tμ¯z-12EAμ¯tn¯z2+μ¯z2μ¯z+ρltxt+n¯t+ltn¯z2+yt+μ¯t+ltμ¯z2+lt2+1-k1∫0ltxtTnzz+12EA3nz2nzz+nzzμz2+2nzμzμzzdz+1-k1∫0ltytTμzz+12EA3μz2μzz+μzznz2+2μznznzzdz+1-k1xtρxt+n¯t+ltn¯zlt-mpgn¯z-12EAn¯z2+μ¯z2n¯z+1-k1ytρyt+μ¯t+ltμ¯zlt-mpgμ¯z-12EAn¯z2+μ¯z2μ¯z;Carefully performing integration by parts leads to the following equation:(20)V˙t=Fl¯+k4l-ld+ρxt+n¯t+ltn¯z2+yt+μ¯t+ltμ¯z2+lt2+ρxt+n¯t+ltn¯zn¯t+1-k1xt+ρyt+μ¯t+ltμ¯zμ¯t+1-k1ytlt+k1FX+k2x-xd-1-k1Tnz0+12EAnz30+12EAnzμz20xt+k1FX+k3y-yd-1-k1Tμz0+12EAμz30+12EAμznz20ytThe above equation suggests that control laws for three motions can be selected as(21)Fl¯=-k4l-ld-ρxt+n¯t+ltn¯z2+yt+μ¯t+ltμ¯z2+lt2-ρxt+n¯t+ltn¯zn¯t+1-k1xt-ρyt+μ¯t+ltμ¯zμ¯t+1-k1yt-kllt(22)FX=-k2x-xd+1-k1Tnz0+1/2EAnz30+1/2EAnzμz20-kxxtk1(23)FY=-k3y-yd+1-k1Tμz0+1/2EAμz30+1/2EAμznz20-kyytk1where kx, ky, and kl are strictly positive constant. It should be noted again that the derived controls are located at the trolley end. The selected controls render time derivative of the Lyapunov function candidate as(24)V˙t=-kllt2-kxxt2-kyyt2<0The inequality suggests that the close loop system is stable in Lyapunov’s sense.


## 4. Simulation Results

Numerical simulations for illustrating the ability of positioning trolley and suppressing payload swing angle of the proposed control are given in this section. Initially, the payload is located at (0,0,0); the system is designed to move the payload to the desired position at (15,20,5). The system simulation parameters are(25)mT=5kg;mP=15kg;EA=0.3N;ρ=0.1kg/m Firstly, the positioning problem is considered regardless of the payload vibration. It can be observed from Figures 2–7 that the desired position is reached; however, there exists payload vibration.Figure 2
Trolley and payload responses in X direction without vibration control.Figure 3
Control forceFx without vibration control.Figure 4
Trolley and payload responses in Y direction without vibration control.Figure 5
Control forceFy without vibration control.Figure 6
Payload response in Z direction without vibration control.Figure 7
Control forceFz without vibration control.Secondly, the proposed control for positioning and vibration suppressing is activated. The simulation results in Figures8–13 show that the effectiveness of the control is confirmed. Control forces are in a practical range. It can be observed that control forces in uncontrolled cases have a tendency of abrupt changing compared to controlled cases. The phenomenon is predicted since vibration of the payload directly affects the trolley motion and leads to changes in control forces.Figure 8
Trolley and payload responses in X direction with vibration control.Figure 9
Control forceFx with vibration control.Figure 10
Trolley and payload responses in Y direction with vibration control.Figure 11
Control forceFy with vibration control.Figure 12
Payload response in Z direction with vibration control.Figure 13
Control forceFZ with vibration control.In addition, because payload vibration is fed back to the trolley, control effort is lower in controlled cases.


## 5. Conclusions

In the paper, position and vibration suppression problems in the gantry crane system with flexible cable are considered. Based on system energy analysis equations of motion that govern the gantry dynamics deforming in two transverse directions with varying cable length is derived according to Hamilton’s extended principle. The process results in a system of ordinary and partial differential equations including cable dynamics and boundary conditions at trolley and payload ends. Control forces that solve the control problem are designed based on Lyapunov’s direct method. The control forces are placed at trolley end of the gantry. Simulations are given to illustrate the effectiveness of the proposed control. System friction, input, and output constraints are the main target in the future research.



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*Source: 9640814-2019-02-11.xml*