Geometric parameters
1. Introduction
Hexapod is a new type of machine tool based on the parallel closed-chain kinematic structure. Compared to the conventional machine tool, parallel mechanism structure offers superior stiffness, lower mass and higher acceleration, resulting from the parallel structural arrangement of the motion systems. Moreover, hexapod has the potential to be highly modular and re-configurable, with other advantages including higher dexterity, simpler and fewer fixtures, and multi-mode manufacturing capabilities.
Initially, hexapod was developed based on the Stewart platform, i.e. the prismatic type of parallel mechanism with the variable leg length. Commercial hexapods, such as VARIAX from Giddings & Lewis, Tornado from Hexel Corp., and Geodetic from Geodetic Technology Ltd., are all based on this structure. One of the disadvantages for the variable leg length structure is that the leg stiffness varies as the leg moves in and out. To overcome this problem, recently the constant leg length hexapod has been envisioned, for instance, HexaM from Toyada (Susuki et al., 1997). Hexaglibe form the Swiss Federal Institute of Techonology (Honegger et al., 1997), and Linapod form University of Stuttgart (Pritschow & Wurst, 1997). Between these two types, the fixed-length leg is stiffer (Tlusty et al., 1999) and, here, becoming popular.
Dynamic modeling and analysis of the parallel mechanisms is an important part of hexapod design and control. Much work has been done in this area, resulting in a very rich literature (Fichter, 1986, Sugimoto, 1987, Do & Yang, 1988, Geng et al., 1992, Tsai, 2000; Hashimoto & Kimura, 1989, Fijany & Bejezy, 1991). However, the research work conducted so far on the inverse dynamics has been focused on the parallel mechanisms with extensible legs.
In this chapter, first, in the inverse dynamics of the new type six d.o.f. hexapods with fixed-length legs, shown in Fig. 1, is developed with consideration of the masses of the moving platform and the legs. (Xi & Sinatra, 2002) This system consists of a moving platform
Finally, for completeness of the dynamic study of the parallel manipulator with the fixed-length legs, the static balancing is studied (Xi et al., 2005).
A great deal of work has been carried out and reported in the literature for the static balancing problem. For example, in the case of serial manipulator, Nathan (Nathan, 1985) and Hervé (Hervé, 1986) applied the counterweight for gravity compensations. Streit et al. (Streit & Gilmore, 1991), (Walsh et al., 1991) proposed an approach to static balanced rotary bodies and two degrees of freedom of the revolute links using springs. Streit and Shin presented a general approach for the static balancing of planar linkages using springs(Streit & Shin, 1980). Ulrich and Kumar presented a method of passive mechanical gravity compensation using appropriate pulley profiles (Ulrich & Kumar, 1991). Kazerooni and Kim presented a method for statically-balanced direct drive arm (Kazerooni & Kim, 1990).
For the parallel manipulator much work was done by Gosselin et al. Research reported in (Gosselin & Wang, 1998) was focused on the design of gravity-compensated of a six–degree-of-freedom parallel manipulator with revolute joints. Each leg with two links is connected by an actuated revolute joint to the base platform and by a spherical joints the moving platform. Two methods are used, one approach using the counterweight and the other using springs. In the former method, if the centre of mass of a mechanism can be made stationary, the static balancing is obtained in any direction of the Cartesian space. In the second approach, if the total energy is kept constant, the mechanism is statically balanced only in the direction of gravity vector. The static balancing conditions are derived for the three-degree-of-freedom spatial parallel manipulator (Wang & Gosselin, 1998) and in similar conditions are obtained for spatial four-degree-of-freedom parallel manipulator using two common methods, namely, counterweights and springs (Wang & Gosselin, 2000).
In this chapter, following the same approach presented by Gosselin, the static balancing of the six d.o.f. platform type parallel manipulator with the fixed-length legs shown is studied. The mechanism can be balanced using the counterweight with a smart design of pantograph. The mechanism can be balanced using the method, i.e., the counterweight with a smart design of pantograph. By this design a constant global center of mass for any configurations of the manipulator is obtained.
Finally, the leg masses become important for hexapods operating at high speeds, such as high-speed machining; then in the future research and development the effect of leg inertia on hexapod dynamics considering high-speed applications will be investigated.
2. Kinematic modeling
2.1. Notation
As shown in Figure 2, this hexapod system consists of a moving platform
The coordinate systems used are a fixed coordinate system O-xyz is attached to the base and a local coordinate system O_{t}-
Furthermore, a local coordinate frame O_{i}-x_{i}y_{i}z_{i} is defined for each leg, with its origin located at the center of the
where
Note that vector
For the purpose of carrying out the inverse dynamics analysis of the hexapod, the following symbols are defined. As shown in Figure 2, C_{i} is the center of mass of the
2.2. Kinematics
Consider one branch of the leg-guideway system, as shown in Figure 2, the following loop equation for
where h and R are the vector and rotation matrix that define the position and orientation of the moving platform relative to the base, respectively,
Since the leg always moves along the guideway, s_{i} can be expressed as
where
where
Substituting eqs.(4 & 5) into eq.(3) and rearranging it yields the following kinematics equations for the fixed-length leg hexapod, for
To obtain the velocity of the moving platform, taking the time derivative of eq. (7) yields
where v and
Furthermore, by taking dot product on both sides of eq.(8) by l_{i}, it leads to
It is well known that the kinematic analysis of parallel manipulator leads to two Jacobian matrices, namely, the forward and the inverse Jacobian (Gosselin & Angeles, 1990). To find the Jacobians for the hexapod under study, rearranging eq.(9) yields the following form
where
where
Eq.(11) defines the differential relationship between the actuator speeds
Provided that B is invertible, the Jacobian matrix of the moving platform
where
for
where
To obtain the acceleration of the moving platform, taking the time derivative of eq. (14) yields
where
where
If the mass of the leg is uniformly distributed, then the center of mass is in its middle. The velocity of the center of mass can be given as
Upon differentiating eq.(22), the acceleration of the center of mass can be given as
To obtain the leg angular velocity and acceleration, denote by E_{i} the
Consider all six legs, it forms a set of linear equations containing the unknowns of the leg angular velocity. There are three components of
In the light of eq.(25), eq. (24) may be rewritten as
where
Solving eq. (26) leads to the expression for the leg angular velocity
Now eq.(29) is substituted back into eq.(22), and the velocity becomes
By examining eqs.(29) and (30), it may be noted that the two terms in the brackets are identical. The first term may be expressed as
where
where 1 is the
The second term in eqs.(29) and (30) can also be expressed in terms of
where
In eq.(35), 0_{3} is the 3-dimensional null vector. The twist of the
where t_{i} is the twist of the ith leg, i.e.
Furthermore, the leg angular acceleration can be obtained by differentiating eq.(26) with respect to time, that is
where
From eq.(38), vector
3. Dynamic modeling
3.1. The natural orthogonal complement method
Prior to performing dynamic modeling of the hexapod, a brief review of the natural orthogonal complement method (Angeles & Lee, 1988) is provided. Consider a system composed of
where
where
In eq. (42), the
where I_{i} is the
If consider all p bodies, the assembled system dynamics equations are given as
where the
and the 6p-dimensional generalized twist t, generalized working wrench
It can be shown that the kinematic constraints hold the following relation with the generalized twist
where
where T is a
By substituting eq.(51) into eq.(50), the following relation can be obtained
where T is the natural orthogonal complement of K. As shown in (Angeles & Lee, 1988, 1989) the non-working vector w^{N} lies in the null space of the transpose of T. Thus, if both sides of eq. (46) are multiplied by T^{T}, in the aid of eqs. (51 & 52), the system dynamics equations can be obtained as
where the
Furthermore, by defining the following generalized forces
the inverse dynamics of the system can be given as
where
3.2. Inverse dynamics
The key in applying the natural orthogonal complement method is to derive the expression for the twist-mapping matrix T, which relates the speeds of the independent variables to the generalized twist. For the hexapod under study, the independent variable s is the vector representing the actuator displacement, with the total number of six, as defined before. The generalized twist is expressed as
Note that t_{1} to t_{6} are the twists for the six legs. Since the twist in eq.(36) is defined at the center of mass of the leg, T_{i} represents the twist-mapping for the legs. For the moving platform, t_{pc} is defined as the center of mass which may be expressed as
Differentiating eq.(59) gives
In the light of eq.(60), the following relation can be obtained
t_{pc} = H_{p} t_{p}
where
In eq.(62), E_{} is the cross-product matrix of
The twist-mapping matrix T for the hexapod under study can be given in the light of eqs.(17), (36) and (62) as
where T is a
4. Simulation
4.1. Geometric and inertial parameters
The geometry of the base and the moving platform is shown in Figure 3.
Accordingly, the coordinates of vector b_{i} with respect to the fixed frame are given as
where L_{b} and l_{b} are the long and short side of the base hexagon,
where L_{p} and l_{p} are the long and short side of the moving platform hexagon, and
S Guideway length | Y Guideway angle | l Leg length | L _{b} Long side BP | l _{b } Short side BP | L _{p } Long side MP | l _{p } Short side MP |
0.60 m | 45 ^{ o 0.50 m 1.00 m 0.09 m 0.50 m 0.09m } | 0.50 m | 1.00 m | 0.09 m | 0.50 m | 0.09m |
m (kg) | Ixx = Iyy (kg m2) | Izz (kg m2) | |
Platform | 3.983 | 0.068 | 0.136 |
Leg | 0.398 | 0.0474 | - |
4.2. Numerical example
A simulation program has been developed using Matlab based on the method described in the previous sections. In terms of computation, as can be seen from eq. (54), the inverse dynamics of the hexapods mainly involves the twist-mapping matrix T and its derivative, which could be computed numerically for each time interval. This way, it is computationally more efficient. To further speed up computation, parallel computation techniques could be used. As shown in Figure 4, the motion part including actuator speeds and accelerations could be computed in parallel to the inertia part including mass matrix I and coupling matrix C. Since the program is done in Matlab, parallel computation is not realized. However, this strategy can certinaly be applied to model-based control using the dynamic equations.
In terms of singularity, as can be shown from eq. (63), the twist-mapping matrix T becomes degenerate when the moving platform Jacobian J_{p} (T_{p} = J_{p} ^{-1}) is singular.
The movement of the moving platform is defined in terms of 3-4-5 polynomials that guarantee zero velocities and zero accelerations at the beginning and at the end. The selection of a smooth motion profile is very important for the hexapod as it is operated under high speeds. The conventional machine tools are run at a maximum velocity of 30m/min with a maximum acceleration of 0.3 g. Hexapods can run at a maximum velocity of 100 m/min with a maximum acceleration over 1 g.
The first simulation is for high speed, with a maximum velocity of 102 m/min. The second simulation is for low high speed with a maximum velocity of 30 m/min. In both cases, the hexapod moves a distance of 0.1m along the z axis. The initial position of the moving platform is at x_{o} = 0, y_{o} = 0 and z_{o} = 0.7m. Figure 4 shows the velocity profiles of the moving platform. Figures 5, 6 and 7 show the displacements, velocities and accelerations of the six actuators, respectively. Figure 8 shows the computed actuator forces. The simulations show that high speed motions result in large actuator forces.
5. Static balancing of the hexapod
The static and dynamic balancing is a classic problem in the theory of machines and mechanisms. In particular, when a mechanism is not statically balanced, the weight of linkage produces force or torque at actuators under static conditions and actuators have to contribute to support the weight of the moving links for any configurations. The problem becomes more serious for the parallel manipulator applied as flight simulator where the weight of the moving platform is very large with respect to the masses of the links. Static balancing also called gravity compensation is important. If the forces/toques exerted by joint actuators are reduced, the full potential of machine will be improved.
In this paragraph, following the same approach presented by Gosselin, the static balancing of the hexapod with the fixed-length legs is studied.
5.1. Static balancing using counterweight
The static balancing of the parallel manipulator under study is investigated using counterweights. The base coordinate frame Oxyz frame, is fixed to the base with Z-axis pointing vertically upward and the moving coordinate frame O'x'y'z' is attached to the moving platform. The Cartesian coordinates used to describe the pose of the platform are as shown in Fig. 9 given by the position of O' with respect to the fixed frame and the orientation of the platform represented by the rotation matrix Q
Using the counterweights, static balancing is obtained if the global center mass of the mechanism is kept stationary at any values of the independent variables. To choose an suitable constant, namely
where r is the position vector of the global mass center, and M is:
where
where
where g is the vector center of mass of the moving platform with respect to the frame O'x'y'z', h is the position of O' with respect to the fixed frame, p_{i} is the position of the spherical joint with respect to the moving coordinate frame, b_{i} is the position of the lower end of the guideway with respect to the fixed frame, l_{i} is the length of the leg, s_{i} can be written, for i=1,…,6, as
where
where
The conditions for static balancing can be given for i=1,..,6, as follows:
From conditions
By condition
Eq.(79) shows that the balancing by counterweight is impossible. If it was substituted in the condition B= 0,
then one can obtain
From eq. (81), it shows that the manipulator could be balanced by a device that provide a force that is
equal to the weight of the links and the platform;
in opposite direction of the weight;
5.2. Static balancing wit a pantograph counterweight
Since it is shown that the static balancing of the examined mechanism is impossible with the help of counterweights, we propose a method to add a pantograph connecting the moving platform O' to the fixed platform O, as shown in Fig. 10. The pantograph is a device that allows to keep two end points on the same line and keep their distance at the centre with a constant ratio. In this application it is possible to use a pantographs with two or more mesh as shown in Fig. 10 and Fig. 11, respectively. In both case the manipulator is balanced. The pantograph is fixed to the moving platform on the point O' by a spherical joint and fixed to the point O by an universal joint. The leg counterweight is shown in Fig.12.
In this case, the mass M becomes,
where
where
where, l_{a} is the center of mass of the pantograph with respect to the fixed frame, l_{a} ^{*} is the pantograph counterweight position with respect to the fixed frame, l_{gi} is the length of the leg counterweight link, l_{i} is the length of the leg, s_{i} can be written, for i=1,...,6, as
In concise form, eq.(84) can be expressed as
where
The conditions for static balancing can be given, for i =1,..,6, as follows
From conditions
From eq. (92), for i=1,..,6, the following is obtained
By condition
one can obtain
Finally, condition B= 0 leads to the following
Eq.(96) shows that the static balancing can be achieved by fixing the global center of the mass of the moving platform, that of the legs and their counterweights at the same position, O'. In order to obtain it, the platform counterweight should be placed in the position:
Simulation is carried out to demonstrate the proposed method. The results are shown in Figs. 13-14, from which it can be seen that the centre of mass of the robot is non-stationary for non balanced case, while it is fixed for the balanced case.
After static balancing the global mass of the device increases by
The negative effect for the dynamic performance by the increasing global mass can be reduced by optimum design of the pantograph. A graph can be arranged to provide such help. Fig. 15 shows the ratios,
which vary respect to the ratio r_{a}
^{*}/ h and l_{gi}
^{*}/ l_{gi} and where I_{i} is the moment of inertia of the leg, I_{i}
^{*} is the moment of inertia of the leg counterweight whit respect of P_{i}, I_{a} is the moment of inertia of the moving platform and I_{a}
^{*} is the moment of inertia of the pantograph counterweight with respect of O. It should be noted that with a suitable design it is possible to reduce
Input | ||
Mobile platform | ||
mass [kg] | short side [mm] | long side [mm] |
8 | 200 | 800 |
Fixed platform 1 | ||
mass [kg] | short side [mm] | long side [mm] |
/ | 100 | 400 |
Fixed platform 2 | ||
mass [kg] | short side [mm] | long side [mm] |
/ | 250 | 1000 |
leg | ||
mass [kg] | l i [mm] | l gi [mm] |
0.5 | 750 | 375 |
Pantograph | ||
mass [kg] | side length [mm] | r a [mm] |
3 | 100 | 0 |
Output | ||
m a * [kg] | m i * [kg] | |
17 | 1 |
7. Conclusion
In this chapter, the inverse dynamics of hexapods with fixed-length legs is analyzed using the natural orthogonal complement method, with considering the mass of the moving platform and those of the legs. A complete kinematics model is developed, which leads to an explicit expression for the twist-mapping matrix. Based on that, the inverse dynamics equations are derived that can be used to compute the required applied actuator forces for the given movement of the moving platform. The developed method has been implemented and demonstrated by simulation.
Successively, the static balancing of hexapods is addressed. The expression of the global center of mass is derived, based on which a set of static balancing equations has been obtained. It is shown that this type of parallel mechanism cannot be statically balanced by counterweights because prismatic joints do not have a fixed point to pivot as revolute joints. A new design is proposed to connect the centre of the moving platform to that of the fixed platform by a pantograph. The conditions for static balancing are derived. This mechanism is able to release the actuated joints from the weight of the moving legs for any configurations of the robot.
In the future research the leg inertia will be include for modeling the dynamics of the hexapod for high-speed applications.
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