In this study, a non-linear dynamics model of Ravigneaux compound planetary gearsets which adopts the intermediate floating component is set up based on concentration parameter. By considering the position errors and eccentric errors, the dynamic load sharing factors of the gearsets are calculated. The relationship between central members radial support stiffness and the dynamic load sharing factors is obtained and the influence of central members radial support stiffness on load sharing characteristic is analyzed. The research results show that central members radial support stiffness affects the gear pairs which are directly contacted to the central members, while the effect is rather small in the gear pairs which are not directly connected. Reducing the radial support stiffness of the central members helps improve the load sharing performance of the system.
Planetary gearsets, a classification of epicyclic gears, have several advantages over fixed-center counter- shaft gear systems, including higher power density (transmitted power to gearsets volume ratio), compactness, ability to achieve multiple speed ratios through different power flow arrangements, and lower gear noise. In addition, axi-symmetric orientation of the planet gears in the gearsets creates negligible radial bearing forces and provides a self-centering capability. This relieves the requirement for bearing support. Based on these advantages, planetary gearsets have been widely used in transportation, aerospace, and energy development areas.
However, these advantages of planetary transmissions rely heavily on the assumption that each pinion carries an equal share of the total torque applied. In the production process, gear manufacturing and assembly variations, as well as design parameters may prevent such equal load sharing characteristics affecting the transmission performance.
The majority of published studies on dynamic load sharing focus on one-stage planetary arrangements. Hidaka, et al., [1-3] studied the planet load sharing of three-planet gearsets to show, both experimentally and theoretically, that perfect load sharing in a three-planet gearsets is achievable only if at least one central member (ring gear, sun gear, or carrier) is allowed to float. The same conclusion was confirmed by Muller . In his 1994 paper, Kahraman  constructed a dynamic mathematical model of a planetary gear stage that could be set to an arbitrary number of planets and corresponding possible gear sizes and tolerance variations, and fixity or not of the sun gear. In another paper , Kahraman considered load sharing of planetary gearsets again, both in a mathematical model and in experimental work, and showed reasonable agreement between his experimental results and mathematical model for a four- planet system. Ligata et al.,  did further work along the lines of the paper of Kahraman  but added the numbers of planets and torque as parametric variables in their experimental study and obtained reasonable agreement with the theory. In Ligata’s work, they demonstrated in an experiment that three- planet systems show excellent load sharing and that four-planet systems with the planets opposite each other show good load sharing between opposed planets, but not so good otherwise. They also mentioned, and one can see in the data plots, that for constant error and other variables, with the torque held constant, load sharing gets better for higher torques.Bodas and Kahraman  used a two- dimensional (2D) deformable-body model of a planetary gearsets and demonstrated theoretically that adding more planets makes the system more sensitive to certain gear and carrier manufacturing errors and assembly variations. They showed that different types of errors acting on each planet could be combined into a total planet error ei representing the effective tangential (in the circumferential direction on the circle formed by planet centers) error of planet i. Singh [9-10] used a three-dimensional (3D) model of the same configuration to obtain similar conclusions. He showed that the directions of the pinhole position errors are important, with the errors in tangential direction having the most critical impact on planet load sharing. He concluded that increasing the number of planets in the system without appropriately tightening the pinhole position tolerances fails to deliver expected planet load reductions. His predictions clearly showed the maximum planet loads for an n-planet (n ≥ 4) system can become higher than the corresponding loads for a planetary gearsets with a smaller number of planets, unless the error magnitudes are appropriately controlled.
All of the models cited above only focus on one-stage planetary gearsets. The demand for fuel economy and more ratios for different speed and torque make vehicle automatic transmissions with compound planetary gearsets very desirable, while few scholars studied the load sharing characteristics of compound planetary gearsets.
In this study, a dynamics model of Ravigneaux compound planetary gearsets, which adopts the intermediate floating component, is set up based on concentration parameter. By considering the influence factors (including central member radial support stiffness), gear eccentric errors, gear position errors and backlash, the load sharing factors of the gearsets are calculated. The curves of the relationships between central members radial support stiffness and the load sharing factors of the gearsets are obtained and the influence of central members radial support stiffness on load sharing characteristic is analyzed.
Ravigneaux compound planetary gear transmissions are based on a simple planetary gear train with a clever combination whose structure is more complex than a simple planetary gear train. The Ravigneaux compound planetary gear system studied in the paper is illustrated in Figure 1. A long planet b connects two planes of double-planet gearsets s1-a-b-r and s2-b-r. Here s1 and s2 are the sun gears, r is the ring gear, and a is the short gear. All planets, a and b, are supported by a single carrier, c. The compound arrangements shown in Figure 1 have four central members, s1, s2, r, and c that can be used as input, output, or reaction members. At any given power flow condition, only three of these four members will have assignments. Therefore, by applying different clutching arrangements, the input, output, and reaction members can be selected in different ways from the four central members of the gearsets. This way, it is possible to obtain permutation P (4, 3) = 24 distinct power flow configurations. With such inherent ratio flexibility, it is feasible to achieve up to five desirable forward and at least one reverse gear ration using the same compound gearsets under different clutching schemes. This allows significant reductions in transmission size and weight making compound planetary units very desirable for such applications.
The dynamic model of this system employs a number of simplifying assumptions.
1. Each gear body is assumed to be rigid and the flexibilities of the gear teeth at each gear mesh interface are modelled by a spring having periodically time-varying stiffness acting along the gear line of action. This mesh stiffness is subject to a clearance element representing gear backlash.
2. Each central member was assumed to move in the torsional θ direction and radial x, y direction, while planets a, b were assumed to move in the torsional θ direction only.
3. As the damping mechanisms at the gear meshes and bearings of a planetary gearsets are not easy to model, viscous gear mesh damping elements are introduced representing energy dissipation of the system.
In Figure 2, the central members s1, s2, r and c, which are mounted on linear elastic bearings with the stiffnesses ks1, ks2, kr, kc, are constrained by torsional linear springs of stiffness magnitude ks1t, ks2t, krt, kct. The magnitudes of torsional stiffness constrains can be chosen accordingly to simulate different power flow arrangements with different fixed central members. Each gear body l (l = s1, s2, r, c, an and bn) is modelled as a rigid disk with a polar mass moment of inertia ll, radius rl and torsional displacement θl. Here θl is the vibrational component of the displacement defined from the nominal rotation of the gear. External torques Ti (I = s1, s2, r and c) are applied to the central members to represent input, output and reaction torque values. The carrier inertia, Ice, is defined in equation 1.
Ic is polar mass moment of inertia of the carrier alone without planets;
N is total number of planet sets a-b in the gearsets,
ma is mass of planets a;
mb is mass of planets b;
rca, rcb are radii of circles passing through the centers of planets a and b, and are defined as:
The mesh of gear pair j (j = s1-an, s2-bn, r-bn and an-bn) is represented by a periodically time-varying stiffness element kj subjected to a piecewise linear backlash function f (δj) that includes a clearance of amplitude bj. A time-varying displacement function of ej (t) is applied along the line of action to account for position error and eccentric error. Loses of lubricated gear contacts are represented by constant viscous damper coefficient cj.
Mesh errors analysis
Pinion position error
Figure 3 illustrates how the position of gear is changed as a function of gear position error. O is the ideal location of s1 center. The sun gear position error of magnitude As1 makes the ideal location point O move to O'. The tangential magnitude of the position error of planet s1, in Figure 3, can be represented by equations 3 and 5.
ωc, φs1, ψn are the angular velocity of carrier, the initial angle of position error and the planet spacing angles.
Similarly, the tangential magnitude of the position error of planet s2, r, an and bn can be represented by:
ν1, ν2, ν3 and φan, φbn, φr are illustrated in in Figure 4.
Figure 5 illustrates how the position of rotation center is changed as a function of eccentric error. The eccentric error s1 of magnitude Es1 moves the gear rotation center from O to O’’. Similar to position error, the tangential magnitude of the position error of gears can be represented by equation 6, where γ is the initial angle of eccentric error.
Dynamic transmission error
By considering both position errors and eccentric errors, the tangential dynamic transmission errors of gear pairs can be represented by ej (t) as
Equations of motion
The relative gear mesh displacements for the s1-an, s2-bn, r-bn, and an-bn are expressed in equations 8 and 9:
ψan, ψbn are the angle between the line which cross the ideal geometric center of an, bn and the coordinate origin O and the x axis of coordinate OXY.
Define Pj and Dj as the elastic and damp meshing force of the gear pairs respectively, which can be expressed as follows.
The piecewise-linear displacement functions are defined as
The equations of motion shown in Figure 2 are written as
mce =mc + N (ma +mb) 
Load sharing behavior
The equations of motion (12 through 18) are nonlinear due to tooth separations and have time-varying stiffness. Since an analytical solution is not available here, a time-domain numerical integration technique is employed to solve equations of motion. The dynamic force on the gear mesh j is then obtained using the expression:
In order to study the load sharing behavior of the system, the dynamic load sharing factor Bj is defined as follows.
Bj is load sharing factor obtained over the entire mesh cycle
bj is load sharing factor obtained for one tooth mesh cycle.
In Figure 6, plots of Bj are given as a function of central member radial support stiffness ki. For instance, when ks1 change from 106 N/m to 109 N/m, the rest central members radial support stiffness ks2 = kr = kc = 109 N/m in Figure 6 (a). Figure 6 (e) shows the how Bj change when ks1, ks2, kr, kc change simultaneously.
1. Figure 6 (a) indicates that with increasing radial support stiffness of the sun gear s1, the dynamic load sharing factors of meshing pairs Bs1an, Bs2bn and Banbn will increase while Brbn almost stay unchanged. Compared with Figure 6 (b-d), Bs1an in Figure 6 (a) is more obviously changed. Floating s1 can improve the load sharing behavior of the system.
2. Similar to Figure 6 (a), Bs1an, Bs2bn and Banbn in Figure 6 (b) increases while Brbn almost stays unchanged with the increasing ks2. Bs2bn changes are obvious compared to Figure 6 (a), (c) and (d). Floating s2 can also improve the load sharing behavior of the system notably.
3. Figure 6 (c) shows that increasing kr affects Brbn to some extent with upward trend while has almost no effect on Bs1an, Bs2bn and Banbn. Floating the ring gear helps to improve the dynamic load sharing characteristics of gear pair rbn, which is directly related to the ring gear.
4. Figure 6 (d) shows that with kc increasing, Bs1an, Bs2bn and Brbn present overall upward trend, while Brbn downward trend, which means the overall load sharing characteristics of the system do not get better by floating the carrier.
5. Figure 6 (e) shows that Bs1an, Bs2bn, Brbn, and Banbn will increase with increasing ks1, ks2, kr and kc.
Floating multiple central members can help to improve the overall load sharing characteristics of the system.
In this paper a non-linear dynamics model of Ravigneaux compound planetary gear train was set up. The model equations allow the analysis of arbitrary number of pinions spaced around the sun gears. Position errors, eccentric errors and tooth separations are included in the equations through nonlinear time- varying relative gear mesh displacement functions.
By calculating the dynamic load sharing factors versus radial support stiffness, the relationship between central members radial support stiffness and the dynamic load sharing factors is obtained and the influence of central members radial support stiffness on load sharing characteristic is analyzed. The research results show that central members radial support stiffness affects the gear pairs which are directly contacted to the central members, while the effect is rather small on the gear pairs which are not directly connected. Reducing the support stiffness of the central members helps improve the load sharing performance of the system. For a Ravigneaux compound planetary gear train which has more than one sun gear, the system can obtain better load sharing behavior by floating both sun gears simultaneously.
1. Hidaka, T., and Terauchi, Y., Dynamic Behavior of Planetary Gear – 1st Report, Load Distribution in Planetary Gear, Bull. JSME, 19, pp. 690–698, 1976.
2. Hidaka, T., Terauchi, Y., and Dohi, K., On the Relation between the Run Out Errors and the Motion of the Center of Sun Gear in a Stoeckicht Planetary Gear,” Bull. JSME, 22, pp. 748–754, 1979..
3. Hidaka, T., Terauchi, Y., and Nagamura, K., Dynamic Behavior of Planetary Gear – 7th Report, Influence of the Thickness of Ring Gear,” Bull. JSME, 22, pp. 1142–1149, 1979.
4. Muller, H. W., Epicyclic Drive Trains, Wayne State University Press, Detroit, 1982.
5. Kahraman, A., Load Sharing Characteristics of Planetary Transmissions, Mech. Mach. Theory, 29(8), pp. 1151–1165, 1994.
6. Kahraman, A., Static Load Sharing Characteristics of Transmission Planetary Gearsets: Model and Experiment, SAE Trans., 108(6), pp. 1954–1963, 1999.
7. Ligata, H., Kahraman, A., and Sing, A., An Experimental Study of the Influence of Manufacturing Errors on Planetary Gear Stresses and Planet Load Sharing, ASME J. Mech. Des., 130, p. 041701, 2008.
8. Bodas, A., and Kahraman, A., Influence of Carrier and Gear Manufacturing Errors on the Static Load Sharing Behavior of Planetary Gearsets, JSME Int. J., Ser. C, 47, pp. 908–915, 2004.
9. Singh, A., Application of a System Level Model to Study the Planetary Load Sharing Behavior, ASME J. Mech. Des., 127, pp. 469–476, 2005.
10. Singh, A., Kahraman, A., and Ligata, H., Internal Gear Strains and Load Sharing in Planetary Transmissions – Model and Experiments, ASME J. Mech. Des., 130(7), p. 072602, 2008.
** Printed with permission of the copyright holder, the American Gear Manufacturers Association, 1001 N. Fairfax Street, Suite 500, Alexandria, Virginia 22314. Statements presented in this paper are those of the authors and may not represent the position or opinion of the AMERICAN GEAR MANUFACTURERS ASSOCIATION.