Mathematical analysis of the meshing performance of planetary roller screws applying different roller thread shapes

Abstract

This article investigates the meshing performance of planetary roller screws applying rollers with circular, elliptical, and parabolic threads. A mathematical model is established for the thread surface, and a method for analytically calculating the meshing points was developed. The meshing point distributions and interference risk area are calculated to analyze the meshing characteristics of the thread shapes considered. The possibility of applying elliptical thread and parabolic thread to the rollers of planetary roller screws in place of the commonly employed circular thread was explored, and elliptical threads were determined to provide better meshing positions, achieve higher transmission speeds, and obtain longer working lifetimes.

Introduction

Planetary roller screws are a type of transmission device that can convert the rotation of a screw into the linear motion of the nut using threaded rollers as mediators. Because of the many advantages of this device, such as high speed, high accuracy, low noise, and long working life, it is widely used in the areas of aerospace, military equipment, numerical control machinery, industrial robots, and medical equipment and is taking the place of hydraulic equipment in many applications.

Considerable research has been conducted regarding the manufacture, parameter matching, kinematic analysis, ¹ and stiffness, friction torque, ² and efficiency calculations of planetary roller screws. ³ However, previous research has been based on the assumption that the screws apply straight threads and the rollers apply circular threads, ⁴ and this assumption has ignored that the shape of the roller thread may have significant effects on the performance of a planetary roller screw.

The transmission of a planetary roller screw relies on the external meshing of the screw thread and the threads of the roller, and this external meshing makes the position of the mesh point reside outside the plane determined by the screw and roller axes (i.e. the cross section). The meshing position is very important for evaluating the meshing performance of a planetary roller screw ⁵ and is determined by the lead angle and the shape of the thread. Our team focuses on the meshing properties of planetary roller screw and has a deep base in calculating the meshing position of planetary roller screw.^7,8 This article raises the issue of applying thread shapes other than the commonly employed circular thread to a planetary roller screw system for the first time and discusses the influence of the thread shape on the meshing performance. This article also develops a method for calculating the meshing position ⁶ between screws with rollers of any thread shape, which may be very useful for design and manufacture of roller screw systems.

Structure of a planetary roller screw

In a planetary roller screw, the screw and nut apply multiple straight threads and the rollers employ single-start threads. The thread shape is determined in the plane through the thread axis. As illustrated in Figure 1, the screw and nut threads share an equivalent thread axis, and the rollers are distributed symmetrically in the circumference between the threads of the screw and nut. There are two sets of intermeshing thread structures in the planetary roller screw: one is the external thread meshing between screw thread and roller screw and the other is internal thread meshing between screw thread and nut thread. The rollers are fixed on the nut by an inner ring gear, a retaining plate, and a wire ring. No axial movement occurs between the rollers and nut, such that transmission is achieved by the meshing behavior of the screw thread and roller threads.

Figure 1.

The structure of a planetary roller screw: ⁸ 1, nut; 2, roller; 3, screw; 4, inner ring gear; 5, retaining plate; 6, wire ring.

Mathematical modeling of the thread surface

The surface of the thread can be defined by the lead angle $\alpha$ , the radius of the pitch circle $R^m$ , and a thread shape function. As shown in Figure 2, the lead angle α means the angle between the medium diameter of the thread and the helix, $\tan \alpha =\mathrm{lead}/2\pi R^m$ . The pitch p of thread S can be established based on $\alpha$ and $R^m$ according to $p=2\pi R^m\tan \alpha$ ; here, we suppose the number of screw threads is 1. As illustrated in Figure 2, the modeling process employs a coordinate system ⁶ $S(O,x,y,z)$ fixed to the thread, where the z-axis direction is equivalent to the thread axis, such that the coordinate $S_1(O_1,x_1,y_1,z_1)$ describes the thread shape, the $x_1{y}_1$ plane is perpendicular to the thread axis, and the z₁-axis is equivalent to the z-axis. The position coordinates are illustrated in Figure 2.

Figure 2.

Thread surface coordinate system.

The homogeneous transformation matrix ${}_0{}^{1}T$ from $S(O,x,y,z)$ to $S_1(O_1,x_1,y_1,z_1)$ is

$${}_0{}^{1}T=\left[\begin{array}{c}\begin{array}{c}\cos \theta \hfill \\ \multicolumn{1}{c}{\sin \theta }\\ \multicolumn{1}{c}{0}\end{array}\hfill \\ \multicolumn{1}{c}{0}\end{array}\begin{array}{c}\begin{array}{c}-\sin \theta \hfill \\ \multicolumn{1}{c}{\cos \theta }\\ \multicolumn{1}{c}{0}\end{array}\hfill \\ \multicolumn{1}{c}{0}\end{array}\begin{array}{c}\begin{array}{c}\sin \theta \hfill \\ \multicolumn{1}{c}{-\cos \theta }\\ \multicolumn{1}{c}{1}\end{array}\hfill \\ \multicolumn{1}{c}{0}\end{array}\begin{array}{c}\begin{array}{c}0\hfill \\ \multicolumn{1}{c}{0}\\ \multicolumn{1}{c}{\theta R^m\tan \alpha }\end{array}\hfill \\ \multicolumn{1}{c}{1}\end{array}\right]$$

(1)

where $\theta$ defines the angle between the x and x₁ axes. The shape of the thread is described in the $x_1{z}_1$ plane. The thread shape function is $z_1=f(x_1)$ , and the homogeneous coordinates of a point P on the thread surface can be expressed as ${\stackrel{\rightharpoonup }{r}}_1$ in $S_1$ as follows

$${\stackrel{\rightharpoonup }{r}}_1=\left[\begin{array}{c}{x}_1\\ 0\\ f\left(x_1\right)\\ 1\end{array}\right]$$

(2)

The homogeneous coordinates in S can therefore be expressed as $\stackrel{\rightharpoonup }{r}$ as follows

$$\stackrel{\rightharpoonup }{r}={}_0{}^{1}T\cdot {\stackrel{\rightharpoonup }{r}}_1=\left[\begin{array}{c}u\cos \theta \\ u\sin \theta \\ f\left(u\right)+\theta R^m\tan \alpha \\ 1\end{array}\right]$$

(3)

Here, u is the radial distance from P to the thread axis.

Taking u and $\theta$ as variables, $\stackrel{\rightharpoonup }{r}$ can represent any point on the thread surface with the following definitions that allow calculation of the normal vector $\stackrel{\rightharpoonup }{N}$

$$\frac{\partial \stackrel{\rightharpoonup }{r}}{\partial u}=\left[\begin{array}{c}\cos \theta \\ \sin \theta \\ f^{\prime }\left(u\right)\end{array}\right]$$

(4)

$$\frac{\partial \stackrel{\rightharpoonup }{r}}{\partial \theta }=\left[\begin{array}{c}-u\sin \theta \\ u\cos \theta \\ R^m\tan \alpha \end{array}\right]$$

(5)

$$\stackrel{\rightharpoonup }{N}=\frac{\partial \stackrel{\rightharpoonup }{r}}{\partial u}\times \frac{\partial \stackrel{\rightharpoonup }{r}}{\partial \theta }=\left[\begin{array}{c}{R}^m\tan \alpha \sin \theta -u{f}^{\prime }\left(u\right)\cos \theta \\ -R^m\tan \alpha \cos \theta -u{f}^{\prime }\left(u\right)\sin \theta \\ u\end{array}\right]$$

(6)

As such, a mathematical model for different thread shapes can be constructed by employing the appropriate thread shape function $z=f(x)$ in the above equations.

Mathematical model of straight thread

Straight thread is widely used as the screw and nut thread in planetary roller screws because it is easily machined and achieves high working accuracy. The shape of the thread is measured in the $x_1{z}_1$ plane, and a sectional view is presented in Figure 3.

Figure 3.

Sectional view of straight thread.

The shape function in the $x_1{z}_1$ plane is

$$z_1=f\left(x_1\right)=\mp x_1\tan \beta \pm H_s$$

(7)

Here, as in the other equations presented unless specified otherwise, the upper “+” or “−” symbol indicates the upper surface of the thread and the lower “+” or “−” symbol indicates the lower surface of the thread with respect to Figure 3. The homogeneous coordinate of the thread shape in $S_1(O_1,x_1,y_1,z_1)$ can be expressed as

$${\stackrel{\rightharpoonup }{r}}_1=\left[\begin{array}{c}u\\ 0\\ \mp u\tan \beta \pm H_s\\ 1\end{array}\right]$$

(8)

and the homogeneous coordinates can be transformed to $S(O,x,y,z)$ according to the following expression

$$\begin{array}{l}\stackrel{\rightharpoonup }{r}={}_0{}^{1}T\cdot {\stackrel{\rightharpoonup }{r}}_1\\ =\left[\begin{array}{c}\cos \theta \\ \begin{array}{c}\sin \theta \\ 0\\ 0\end{array}\end{array}\begin{array}{c}-\sin \theta \\ \begin{array}{c}\cos \theta \\ 0\\ 0\end{array}\end{array}\begin{array}{c}0\\ \begin{array}{c}0\\ 1\\ 0\end{array}\end{array}\begin{array}{c}0\\ \begin{array}{c}0\\ \theta R^m\tan \alpha \\ 1\end{array}\end{array}\right]\left[\begin{array}{c}u\\ 0\\ \mp u\tan \beta \pm H_s\\ 1\end{array}\right]\\ =\left[\begin{array}{c}u\cos \theta \\ u\sin \theta \\ \mp u\tan \beta \pm H_s+\theta R^m\tan \alpha \\ 1\end{array}\right]\end{array}$$

(9)

Differentiating equation (9) with respect to u and $\theta$ provides the following relationships

$$\frac{\partial \stackrel{\rightharpoonup }{r}}{\partial u}=\left[\begin{array}{c}\cos \theta \\ \sin \theta \\ \mp \tan \beta \end{array}\right]$$

(10)

$$\frac{\partial \stackrel{\rightharpoonup }{r}}{\partial \theta }=\left[\begin{array}{c}-u\sin \theta \\ u\cos \theta \\ R^m\tan \alpha \end{array}\right]$$

(11)

The normal vector at a point on a straight thread surface can therefore be calculated as follows

$$\stackrel{\rightharpoonup }{N}=\frac{\partial \stackrel{\rightharpoonup }{r}}{\partial u}\times \frac{\partial \stackrel{\rightharpoonup }{r}}{\partial \theta }=\left[\begin{array}{c}{R}^m\tan \alpha \sin \theta \pm u\tan \beta \cos \theta \\ -R^m\tan \alpha \cos \theta \pm u\tan \beta \sin \theta \\ u\end{array}\right]$$

(12)

Mathematical model of circular thread

Circular thread is typically used as the roller thread for readily available planetary roller screw products. A sectional view of circular thread is shown in Figure 4 in terms of the radius of the thread contour circle R from its center point O_c of height H_c along the z₁-axis to the center of thread O₁, and an angle γ with respect to the z₁-axis can be used to represent different positions on the thread contour.

Figure 4.

Sectional view of circular thread.

In the $x_1{z}_1$ plane, the circular thread contour can be expressed as

$$x_1^2+{(z_1\pm H_c)}^2=R^2$$

(13)

The homogeneous coordinates representing the circular thread contour in $S_1(O_1,x_1,y_1,z_1)$ can be expressed as

$${\stackrel{\rightharpoonup }{r}}_1=\left[\begin{array}{c}R\sin \gamma \\ 0\\ \pm R\cos \gamma \mp H_c\\ 1\end{array}\right]$$

(14)

and the homogeneous coordinates can be transformed to $S(O,x,y,z)$ as follows

$$\begin{array}{l}\stackrel{\rightharpoonup }{r}={}_0{}^{1}T\cdot {\stackrel{\rightharpoonup }{r}}_1\\ =\left[\begin{array}{c}\cos \theta \\ \begin{array}{c}\sin \theta \\ 0\\ 0\end{array}\end{array}\begin{array}{c}-\sin \theta \\ \begin{array}{c}\cos \theta \\ 0\\ 0\end{array}\end{array}\begin{array}{c}0\\ \begin{array}{c}0\\ 1\\ 0\end{array}\end{array}\begin{array}{c}0\\ \begin{array}{c}0\\ \theta R^m\tan \alpha \\ 1\end{array}\end{array}\right]\left[\begin{array}{c}R\sin \gamma \\ 0\\ \pm R\cos \gamma \mp H_c\\ 1\end{array}\right]\\ =\left[\begin{array}{c}R\cos \theta \sin \gamma \\ R\sin \theta \sin \gamma \\ \pm R\cos \gamma \mp H_c+\theta R^m\tan \alpha \\ 1\end{array}\right]\end{array}$$

(15)

Here, because $u=R\sin \gamma$ , the coordinates can be simplified as

$$\stackrel{\rightharpoonup }{r}=\left[\begin{array}{c}u\cos \theta \\ u\sin \theta \\ \pm \sqrt{R^2-u^2}\mp H_c+\theta R^m\tan \alpha \\ 1\end{array}\right]$$

(16)

The normal vector of any point on the circular thread surface $\stackrel{\rightharpoonup }{N}$ can then be calculated as follows

$$\stackrel{\rightharpoonup }{N}=\frac{\partial \stackrel{\rightharpoonup }{r}}{\partial u}\times \frac{\partial \stackrel{\rightharpoonup }{r}}{\partial \theta }=\left[\begin{array}{c}{R}^m\tan \alpha \sin \theta \pm \frac{u^2\cos \theta }{\sqrt{R^2-u^2}}\\ -R^m\tan \alpha \cos \theta \pm \frac{u^2\sin \theta }{\sqrt{R^2-u^2}}\\ u\end{array}\right]$$

(17)

Mathematical model of elliptical thread

Elliptical thread can also be employed for roller thread, which is also measured in the $x_1{z}_1$ plane, and a sectional view is shown in Figure 5. The center of the ellipse is at the origin O₁ of the coordinate system, the long axis of length a lies on the x₁-axis, and the short axis of length b lies on the z₁-axis.

Figure 5.

Sectional view of elliptical thread.

In the $x_1{z}_1$ plane, the elliptical thread contour can be expressed as

$$\frac{x_1^2}{a^2}+\frac{z_1^2}{b^2}=1$$

(18)

The homogeneous coordinates representing the elliptical thread contour in $S_1(O_1,x_1,y_1,z_1)$ can be expressed as

$${\stackrel{\rightharpoonup }{r}}_1=\left[\begin{array}{c}a\cos \gamma \\ 0\\ b\sin \gamma \\ 1\end{array}\right]$$

(19)

and the homogeneous coordinates can be transformed to $S(O,x,y,z)$ as follows

$$\begin{array}{l}\stackrel{\rightharpoonup }{r}={}_0{}^{1}T\cdot {\stackrel{\rightharpoonup }{r}}_1\\ =\left[\begin{array}{c}\cos \theta \\ \begin{array}{c}\sin \theta \\ 0\\ 0\end{array}\end{array}\begin{array}{c}-\sin \theta \\ \begin{array}{c}\cos \theta \\ 0\\ 0\end{array}\end{array}\begin{array}{c}0\\ \begin{array}{c}0\\ 1\\ 0\end{array}\end{array}\begin{array}{c}0\\ \begin{array}{c}0\\ \theta R^m\tan \alpha \\ 1\end{array}\end{array}\right]\left[\begin{array}{c}a\sin \gamma \\ 0\\ b\cos \gamma \\ 1\end{array}\right]\\ =\left[\begin{array}{c}a\cos \theta \cos \gamma \\ a\sin \theta \cos \gamma \\ b\sin \gamma +\theta R^m\tan \alpha \\ 1\end{array}\right]\end{array}$$

(20)

Here, because $u=a\cos \gamma$ , the coordinates can be simplified as

$$\stackrel{\rightharpoonup }{r}=\left[\begin{array}{c}u\cos \theta \\ u\sin \theta \\ \pm \frac{b}{a}\sqrt{a^2-u^2}+\theta R^m\tan \alpha \\ 1\end{array}\right]$$

(21)

The normal vector of any point on the elliptical thread surface $\stackrel{\rightharpoonup }{N}$ can then be calculated as follows

$$\stackrel{\rightharpoonup }{N}=\frac{\partial \stackrel{\rightharpoonup }{r}}{\partial u}\times \frac{\partial \stackrel{\rightharpoonup }{r}}{\partial \theta }=\left[\begin{array}{c}{R}^m\tan \alpha \sin \theta \pm \frac{b{u}^2\cos \theta }{a\sqrt{a^2-u^2}}\\ -R^m\tan \alpha \cos \theta \pm \frac{b{u}^2\sin \theta }{a\sqrt{a^2-u^2}}\\ u\end{array}\right]$$

(22)

Mathematical model of parabolic thread

Figure 6 provides a sectional view of a parabolic thread applied to a roller with a contour height H_p measured in the $x_1{z}_1$ plane.

Figure 6.

Sectional view of parabolic thread.

In the $x_1{z}_1$ plane, the parabolic thread contour can be expressed as

$$z_1={tx}_1^2+H_p$$

(23)

where t is the parabola shape parameter. The homogeneous coordinates representing the parabolic thread contour in $S_1(O_1,x_1,y_1,z_1)$ can be expressed as

$${\stackrel{\rightharpoonup }{r}}_1=\left[\begin{array}{c}u\\ 0\\ t{u}^2+H_p\\ 1\end{array}\right]$$

(24)

and the homogeneous coordinates can be transformed to $S(O,x,y,z)$ as follows

$$\begin{array}{l}\stackrel{\rightharpoonup }{r}={}_0{}^{1}T\cdot {\stackrel{\rightharpoonup }{r}}_1\\ =\left[\begin{array}{c}\cos \theta \\ \begin{array}{c}\sin \theta \\ 0\\ 0\end{array}\end{array}\begin{array}{c}-\sin \theta \\ \begin{array}{c}\cos \theta \\ 0\\ 0\end{array}\end{array}\begin{array}{c}0\\ \begin{array}{c}0\\ 1\\ 0\end{array}\end{array}\begin{array}{c}0\\ \begin{array}{c}0\\ \theta R^m\tan \alpha \\ 1\end{array}\end{array}\right]\left[\begin{array}{c}u\\ 0\\ t{u}^2+H_p\\ 1\end{array}\right]\\ =\left[\begin{array}{c}u\cos \theta \\ u\sin \theta \\ t{u}^2+H_p+\theta R^m\tan \alpha \\ 1\end{array}\right],\end{array}$$

(25)

The normal vector of any point on the parabolic thread surface $\stackrel{\rightharpoonup }{N}$ can then be calculated as follows

$$\stackrel{\rightharpoonup }{N}=\frac{\partial \stackrel{\rightharpoonup }{r}}{\partial u}\times \frac{\partial \stackrel{\rightharpoonup }{r}}{\partial \theta }=\left[\begin{array}{c}{R}^m\tan \alpha \sin \theta -2t{u}^2\cos \theta \\ -R^m\tan \alpha \cos \theta -2t{u}^2\sin \theta \\ u\end{array}\right]$$

(26)

Calculation of the meshing position

The screw thread and roller threads of a planetary roller screw externally mesh at their pitch diameters, and the thread axes are parallel. The meshing condition is that the position vector of the meshing point on the screw thread surface equals that on the roller thread surface, and their normal vectors lie in the same direction. Meshing equations can therefore be constructed to calculate the meshing point based on the meshing condition as follows

$$\{\begin{array}{c}{\stackrel{\rightharpoonup }{r}}_s={\stackrel{\rightharpoonup }{r}}_r\\ {\stackrel{\rightharpoonup }{N}}_s=\lambda {\stackrel{\rightharpoonup }{N}}_r\left(\lambda \ne 0\right)\end{array}$$

(27)

Here, and for other variables used henceforth unless otherwise indicated, the subscripts s and r represent the parameters of the screw and roller, respectively.

A common method for calculating the meshing position is building the meshing equations with a given distance between the screw and roller axes and calculating the meshing radii and meshing angles as shown in Figure 7. The equations built applying this method are very complex and are often solved using numerical methods. While a numerical method can be used to establish accurate mesh point positions for a planetary roller screw with given parameters, numerical calculations have serious limitations when working with the parametric equations appearing in the design and development process.

Figure 7.

Meshing point measured in the plane perpendicular to the screw and roller axes.

In this study, several parameters are formalized to simplify the meshing equations and to make it possible to establish analytical solutions of the meshing positions as follows. The meshing point occurs on the x_s-axis (Figure 7), which means that ${\theta }_s=0$ and $u_s$ is taken as a given parameter. The equation ${\stackrel{\rightharpoonup }{N}}_s=\lambda {\stackrel{\rightharpoonup }{N}}_r$ is applied to calculate $u_r$ and ${\theta }_r$ , and the distance between the screw and roller axes d is calculated based on ${\stackrel{\rightharpoonup }{r}}_s={\stackrel{\rightharpoonup }{r}}_r$ . Finally, the positions of the screw thread, the roller thread, and the meshing point are determined. The meshing position is calculated using the upper surface of the screw thread and the lower surface of the roller thread, where straight thread is applied for the screw thread and the roller thread may be circular, elliptical, or parabolic.

The normal vectors of the meshing points at the thread surfaces of the screw and roller can be expressed as follows

$${\stackrel{\rightharpoonup }{N}}_s=\left[\begin{array}{c}{u}_s\tan {\beta }_s\\ -R_s^m\tan {\alpha }_s\\ u_s\end{array}\right]$$

(28)

$${\stackrel{\rightharpoonup }{N}}_r=\left[\begin{array}{c}{R}_r^m\tan {\alpha }_r\sin {\theta }_r-u_r\cos {\theta }_r{f}^{\prime }\left(u_r\right)\\ -R_r^m\tan {\alpha }_r\cos {\theta }_r-u_r\sin {\theta }_r{f}^{\prime }\left(u_r\right)\\ u_r\end{array}\right]$$

(29)

By substituting equations (28) and (29) into ${\stackrel{\rightharpoonup }{N}}_s=\lambda {\stackrel{\rightharpoonup }{N}}_r$ , the meshing equations can be constructed as follows

$$R_r^m\tan {\alpha }_r\sin {\theta }_r-u_r\cos {\theta }_{r}f\prime \left(u_r\right)=u_r\tan {\beta }_s$$

(30a)

$$R_r^m\tan {\alpha }_r\cos {\theta }_r+u_r\sin {\theta }_{r}f\prime \left(u_r\right)=\frac{u_r{R}_s^m\tan {\alpha }_s}{u_s}$$

(30b)

$$u_s=\lambda u_r$$

(30c)

Summing the squares of the two equations in equation (30) results in an equation in which $u_r$ is the only unknown quantity, which is given as follows

$$\begin{array}{l}{u}_r^{2}f\prime {\left(u_r\right)}^2-u_r^2\tan {\beta }_s^2-\frac{u_r^2{\left(R_s^m\right)}^2\tan {\alpha }_s^2}{u_s^2}\\ +{\left(R_r^m\right)}^2\tan {\alpha }_r^2=0\end{array}$$

(31)

We can solve for $u_r$ by substituting $z_1=f(x_1)$ into equation (31) as follows

$$u_r=\frac{u_s{R}_r^m\tan {\alpha }_r}{\sqrt{R_s^{m2}\tan {\alpha }_s^2+u_s^2\tan {\beta }_s^2-u_s^{2}f\prime {\left(u_r\right)}^2}}$$

We can solve ${\theta }_r$ by substituting equation (30b) × sinθ_r−equation (30a) × cosθ_r as follows

$$u_{r}f\prime \left(u_r\right)=\frac{u_r{R}_s^m\tan {\alpha }_s}{u_s}\sin {\theta }_r-u_r\tan {\beta }_s\cos {\theta }_r$$

(32)

We can then solve for ${\theta }_r$ by equation (32) as follows

$${\theta }_r=\arcsin \left(\frac{f^{\prime }\left(u_r\right)u_s}{\sqrt{{\left(R_s^m\tan {\alpha }_s\right)}^2+u_s^2\tan {\beta }_s^2}}\right)-\arctan \left(\frac{R_s^m\tan {\alpha }_s}{u_s\tan {\beta }_s}\right)$$

(33)

According to equation (31), we can achieve the result of $f\prime (u_r)$ as follows

$$f\prime \left(u_r\right)=\sqrt{u_s^2\tan {\beta }_s^2+{\left(R_s^m\tan {\alpha }_s\right)}^2-\frac{u_s^2{R}_s^{m2}\tan {\alpha }_r^2}{u_r^2}}$$

(34)

Because the meshing radius and the lead radius of the screw and roller are almost same, and the screw and the roller often use the same tooth angle, in the case of $u_r\approx R_r^m$ , $u_s\approx R_s^m$ , $\tan {\beta }_s\approx \tan {\beta }_r$ , equation (34) can be approximated as follows

$$\begin{array}{l}{\theta }_r=\arcsin \left(\frac{u_s{R}_r^m\tan {\alpha }_r}{u_r\sqrt{{\left(R_s^m\tan {\alpha }_s\right)}^2+u_s^2{\tan }^2{\beta }_s}}\right)\\ -\arctan \left(\frac{R_s^m\tan {\alpha }_s}{u_s\tan {\beta }_s}\right)\end{array}$$

(35)

The relative position between the screw and roller can now be calculated based on $u_r$ and ${\theta }_r$ . As shown in Figure 8, the position of the meshing point in the roller coordinate system $S_r(O_r,x_r,y_r,z_r)$ is

$${\stackrel{\rightharpoonup }{r}}_r=\left[\begin{array}{c}{u}_r\cos {\theta }_r\\ u_r\sin {\theta }_r\\ f\left(u_r\right)+{\theta }_r{R}_r^m\tan {\alpha }_r\end{array}\right]$$

(36)

and the position of the meshing point in the screw coordinate system $S_s(O_s,x_s,y_s,z_s)$ is

$${\stackrel{\rightharpoonup }{r}}_s=\left[\begin{array}{c}{u}_s\\ 0\\ \left(R_s^m-u_s\right)\tan {\beta }_s\end{array}\right]$$

(37)

Figure 8.

The coordinates of meshing points for the proposed analytical calculation.

The relative position between the screw and roller is then equal to the relative position between $S_s(O_s,x_s,y_s,z_s)$ and $S_r(O_r,x_r,y_r,z_r)$ , which can be calculated as follows

$${\stackrel{\rightharpoonup }{r}}_{s-r}={\stackrel{\rightharpoonup }{r}}_s-{\stackrel{\rightharpoonup }{r}}_r=\left[\begin{array}{c}{u}_s-u_r\cos {\theta }_r\\ -u_r\sin {\theta }_r\\ \left(R_s^m-u_s\right)\tan {\beta }_s-f\left(u_r\right)-{\theta }_r{R}_r^m\tan {\alpha }_r\end{array}\right]$$

(38)

The distance between the screw and roller axes can be calculated as $d=\sqrt{u_s^2+u_r^2-2u_s{u}_r\cos {\theta }_r}$ .

The corresponding meshing radius can then be established by applying the above method using a circular, elliptical, or parabolic thread shape function. The equation for calculating the meshing radius of a circular thread roller is as follows

$$u_{\mathrm{rc}}=\sqrt{\frac{-N_c\pm \sqrt{N_c^2-4M_c{L}_c}}{2M_c}}$$

(39)

In equation (39)

$$\begin{array}{c}{M}_c={\left(R_s^m\right)}^2\tan {\alpha }_s^2+u_s^2+u_s^2{\tan }^2{\beta }_s\hfill \\ N_c=-u_s^2{\left(R_r^m\right)}^2{\tan }^2{\alpha }_r-R^2{u}_s^2{\tan }^2{\beta }_s-R^2{\left(R_s^m\right)}^2{\tan }^2{\alpha }_s\hfill \\ L_c=R^2{u}_s^2{\left(R_r^m\right)}^2{\tan }^2{\alpha }_r\hfill \end{array}$$

(39)

The equation for calculating the meshing radius of an elliptical thread roller is as follows

$$u_{\mathrm{re}}=\sqrt{\frac{-N_e\pm \sqrt{N_e^2-4M_e{L}_e}}{2M_e}}$$

(40)

In equation (40)

$$\begin{array}{c}{M}_e=a^2{\left(R_s^m\right)}^2\tan {\alpha }_s^2+b^2{u}_s^2+a^2{u}_s^2{\tan }^2{\beta }_s\hfill \\ N_e=-a^2{u}_s^2{\left(R_r^m\right)}^2{\tan }^2{\alpha }_r-a^4{u}_s^2{\tan }^2{\beta }_s-{\left(R_s^m\right)}^2{\tan }^2{\alpha }_s{a}^4\hfill \\ L_e=a^4{u}_s^2{\left(R_r^m\right)}^2{\tan }^2{\alpha }_r\hfill \end{array}$$

(40)

The equation for calculating the meshing radius of a parabolic thread roller is as follows

$$u_{\mathrm{rp}}=\sqrt{\frac{-N_p\pm \sqrt{N_p^2-4M_p{L}_p}}{2M_p}}$$

(41)

In equation (41)

$$\begin{array}{c}{M}_p=4t^2{u}_s^2\hfill \\ N_p=-{\left(R_s^m\right)}^2\tan {\alpha }_s^2-u_s^2{\tan }^2{\beta }_s\hfill \\ L_p=u_s^2{\left(R_r^m\right)}^2{\tan }^2{\alpha }_r\hfill \end{array}$$

(41)

The meshing angle can be obtained by substituting the calculated meshing radius into equation (35). The positions of the screw thread and roller thread can be calculated based on the calculated meshing radius and meshing angle.

Simulation of thread meshing

This section will employ specific data to calculate and analyze the meshing positions of a planetary roller screw applying rollers with different thread shapes. The data used in the simulations are listed in Table 1. The data in Table 1 are input into the equations derived in section “Calculation of the meshing position,” and MATLAB is employed to simulate the meshing between screw and roller.

Table 1.

Parameters of planetary roller screws with different thread shapes.

Pitch radius of the screw	Pitch radius of the roller	Lead of screw thread	Pitch of roller thread	Number of screw threads
9.75 mm	3.25 mm	10 mm	2 mm	5
Circular thread parameters	Radius of thread contour circle R		Center height of thread contour circle $H_c$
	4.5 mm		3 mm
Elliptical thread parameters	Long axis of contour ellipse a		Short axis of contour ellipse b
	3.5 mm		1.5 mm
Parabolic thread parameters	Parabola shape parameter t		Height of parabola $H_p$
	0.155		1.9 mm

Figure 9 shows the changing positions of meshing points on roller thread surfaces with various shapes following a change of $u_s$ from 9.5 to 10 mm, as indicated by the short colored lines in the graph. The span of $u_s$ contains any possible $u_s$ value from the root to the crest of the thread; however, the positions of the meshing points exhibit only very small variations. This indicates that the value of $u_s$ has little effect on the position of the meshing point. The three thread shapes considered (circular thread, elliptical thread, and parabolic thread) have relatively steady meshing radii on the roller thread.

Figure 9.

Meshing points indicated by the colored lines under different $u_s$ from 9.5 to 10 mm (6 data points).

In the actual meshing process, the value of $u_s$ deviates little from the pitch radius, and, as can be seen from Figure 9, the pitch radius would not seriously influence the meshing position. Therefore, using u_s = 9.75 mm in the simulation accords with actual conditions and meets the requirements of theoretical analysis.

Positions of meshing points under varying parameters

When the pitch diameters of the screw and rollers are fixed, the most important parameters are the pitch and number of threads. Rollers apply single-start thread, and screws apply multiple threads.

The meshing points of the three different thread shapes were calculated using different pitch values from 0 to 10 mm in intervals of 0.5 mm which are applied to both screw threads and roller threads with all other parameters being those listed in Table 1. The resulting variation in the meshing points is shown by the colored lines in Figure 10.

Figure 10.

Meshing points indicated by the colored lines under different pitch values from 0 to 10 mm in 0.5 mm intervals (20 data points).

As shown in Figure 10, when the pitch changes from 0 to 10 mm, the varying meshing points on the roller thread surfaces represent curves away from the thread axis. When the value of the pitch is 0, the threads become parallel ring structures, and the meshing points are close to the pitch diameter. With increasing pitch, the meshing radii on the roller thread surfaces increase, and the meshing points move toward the crest of the thread. The crest of the thread has a smaller thread tooth thickness and poorer bearing capacity. As a result, meshing at this location may cause larger deformations or even failure. The meshing points on the circular thread move toward the crest at a moderate rate with increasing pitch, whereas the meshing points on the elliptical thread move at a much slower rate and maintain a position close to the pitch diameter. The meshing points on the parabolic thread rapidly move away from the axis and beyond the thread surface. As such, elliptical thread rollers are observed to have better meshing locations that allow the application of a larger pitch, which supports a larger transmission speed. Therefore, a comparison with the widely applied circular thread rollers indicates that planetary roller screws applying elliptical thread rollers would provide better performance and achieve higher transmission speeds.

As shown in Figure 11, with the number of screw threads increasing from 1 to 10, the meshing points move toward the crest of the thread. Like the results obtained when varying the pitch, the elliptical thread exhibits the best meshing locations and the parabolic thread the worst. Relative to the results obtained with increasing pitch, a larger number of screw threads impacts the meshing points to a lesser extent.

Figure 11.

Meshing points indicated by the colored lines under different number of screw threads from 1 to 10 (10 points).

It has been shown that applying elliptical thread rollers can help improve the meshing performance of planetary roller screws and is especially suitable for applications employing large pitch and a greater number of screw threads to achieve high speed transmission. Elliptical thread rollers demonstrate a stable meshing radius and a meshing point close to the pitch diameter, which is advantageous for improving the bearing capacity of planetary roller screws.

Analysis of interference risk

In the area around a meshing point, the distance between the two meshing surfaces is very small. As such, interference may occur in this area in the presence of a large deformation or wear. This area is therefore denoted as the interference risk area. In addition to the risk of interference, the small space between the meshing surfaces in this area is not conductive to the dissipation of heat, and, therefore, a smaller interference risk area is beneficial for both lowering the risk of interference and increasing the working life.

This study employs an interference function $f_{\mathrm{int}}(R,\theta )$ to determine the size of the interference risk area. $f_{\mathrm{int}}(R,\theta )$ can be established based on equations (3), (31), and (33) as follows

$$\begin{array}{l}{f}_{int}\left(R,\theta \right)=\left(R_s^m-R\right)\tan {\beta }_s+\theta A_s-f\left(R_r\right)-{\Theta }_r{A}_r\\ -\left(R_s^m-u_s\right)\tan {\beta }_s+f\left(u_r\right)+{\theta }_r{A}_r\end{array}$$

(42)

Here, $R_r$ and ${\Theta }_r$ are the polar radius and polar angle, respectively, in the roller coordinate system, which can be expressed as follows

$$\{\begin{array}{c}{R}_r=\sqrt{{(R\cos \theta -u_s+u_r\cos {\theta }_r)}^2+{(R\sin \theta +u_r\sin {\theta }_r)}^2}\hfill \\ \multicolumn{1}{c}{{\Theta }_r=\pi +\arctan \left(\frac{R\sin \theta +u_r\sin {\theta }_r}{R\cos \theta -u_s+u_r\cos {\theta }_r}\right)}\end{array}$$

(43)

At the meshing point, the value of the interference function is 0, that is, $f_{\mathrm{int}}(u_r,0)=0$ , and we define the area satisfying $|f_{\mathrm{int}}(R,\theta )|\le \xi$ as the interference risk area, where $\xi$ is the critical interference coefficient determined by the allowable error.

The data in Table 1 were employed to calculate the meshing location, which were substituted into equation (42) with $\xi =0.005\mathrm{mm}$ to calculate the extent of the interference risk area for the three thread shapes considered, as shown in Figure 12.

Figure 12.

The interference risk area of the thread shapes considered.

As shown in Figure 12, the elliptical thread exhibits the smallest interference risk area and the parabolic thread the largest. This demonstrates that a planetary roller screw applying elliptical thread would have lower risk of interference and enhanced heat dissipation, thereby prolonging its working life.

Conclusion

A mathematical model of screw/roller thread was constructed, and a method for analytically calculating the meshing points was developed. The proposed method was demonstrated to be applicable to planetary roller screws applying any type of roller thread. Based on the meshing calculations, the study explored the possibility of applying elliptical thread and parabolic thread to the rollers of planetary roller screws in place of the commonly employed circular thread. The meshing performance of planetary roller screws was also analyzed from the viewpoints of the meshing points distribution and interference risk, and the application of elliptical thread rollers was found to provide the best performance. Planetary roller screws applying elliptical thread would provide better meshing positions, achieve higher transmission speeds, and obtain longer working lifetimes.