Eight-Bar Elbow Joint Exoskeleton Mechanism

Abstract

This paper deals with the design and kinematic analysis of a novel mechanism for the elbow joint of an upper-limb exoskeleton, with the aim of helping operators, in terms of effort and physical resistance, in carrying out heavy operations. In particular, the proposed eight-bar elbow joint exoskeleton mechanism consists of a motorized Watt I six-bar linkage and a suitable RP dyad, which connects mechanically the external parts of the human arm with the corresponding forearm by hook and loop velcro, thus helping their closing relative motion for lifting objects during repetitive and heavy operations. This relative motion is not a pure rotation, and thus the upper part of the exoskeleton is fastened to the arm, while the lower part is not rigidly connected to the forearm but through a prismatic pair that allows both rotation and sliding along the forearm axis. Instead, the human arm is sketched by means of a crossed four-bar linkage, which coupler link is considered as attached to the glyph of the prismatic pair, which is fastened to the forearm. Therefore, the kinematic analysis of the whole ten-bar mechanism, which is obtained by joining the Watt I six-bar linkage and the RP dyad to the crossed four-bar linkage, is formulated to investigate the main kinematic performance and for design purposes. The proposed algorithm has given several numerical and graphical results. Finally, a double-parallelogram linkage, as in the particular case of the Watt I six-bar linkage, was considered in combination with the RP dyad and the crossed four-bar linkage by giving a first mechanical design and a 3D-printed prototype.

1. Introduction

Exoskeleton design, in particular for devices like upper limb exoskeletons, is aimed to carefully replicate the human joint movements. Achieving this accuracy involves understanding the kinematics of the human body and translating it into appropriate mathematical models. This, together with an adequate fit, size, and weight, determines the goodness of the designed device itself. In order to be able to design these devices, it is therefore necessary to first understand what the real movements are and make an appropriate schematization. In particular, the human arm is composed of three joints: the shoulder, the elbow, and the wrist. From a kinematic point of view, the human arm can be schematized with an open kinematic chain with 7 degrees of freedom (DOF), as reported in [1,2]. Specifically, there are 3 DOF in the shoulder (ball and socket joint), 1 DOF in the elbow (revolute joint), and 3 DOF in the wrist (spherical joint). Among the upper limb exoskeletons there are many examples of 7 DOF kinematic chains, which try to reproduce the real kinematic scheme of the human arm [3,4], but there are also examples of kinematic chains with a lower number of degrees of freedom, such as those at 3 DOF [5,6] or 6 DOF [7,8]. Over the years, exoskeletons have undergone considerable variations not only in terms of choice of kinematic chain but also in terms of fields of application. In fact, historically, they were born in the military field with the aim of increasing the performance of soldiers in terms of resistance and strength, but are widely used both in the rehabilitation and in the industrial fields. In particular, in the rehabilitation sector, upper limb exoskeletons have undergone considerable development in the last decade [9,10,11,12,13,14]. Exoskeletons for the upper limb also differ in relation to the actuation system. Considering that they can also be totally passive or underactuated, most of them have electric actuation [15], even if there are also examples of exoskeletons that have a pneumatic actuation [16]. In the design of upper limb exoskeletons, different types of mechanisms are used. They typically present serial kinematic chains, but there are also examples of exoskeletons that have parallel architectures [17], rather than the presence of gears [18] or tendon-driven systems [19,20].

In recent years, it is also possible to find an effort in the design of systems that are as anthropomorphic, as possible, as proposed by Bai in [21] regarding the shoulder joint which approximates a spherical motion. The synthesis of a spherical rigid body guidance for five-poses can be found in [22]. Furthermore, soft robotics has been gaining traction in the field of exoskeletons. Soft robotic exosuits provide a comfortable and portable alternative to rigid exoskeletons for upper limb support, enhancing user comfort and freedom of movement, as reported in [23].

Also, with regard to the elbow, there are several solutions that try to consider the fact that it cannot strictly be represented with a simple revolute joint [24,25,26,27,28,29]. It is clear that in order to design a mechanism that is able to approximate as faithfully as possible the real movement of the human elbow, it is necessary to perform an accurate analysis of the movement. For this purpose, centrodes, which represent the exact law of motion that the designer wants to approximate, are useful.

In the literature, Beadle and O’Brien conducted the first experiments on the experimental detection of the human elbow centrodes [30], taking inspiration from Freudenstein, who years earlier had pioneered the usefulness of centrodes in the analysis of human knee movement [31]. The use of centrodes as a kinematic analysis tool can be found in different fields of engineering. As proposed by the authors in [32], centrodes can be used as an analysis tool to validate knee joint exoskeleton mechanism accuracy. They can also be used to investigate the kinematic characteristics of classical mechanisms, but their field of application is transversal and also related to other sectors, such as machine tools [33]. This analysis tool, combined with that of the Bresse circles [34,35] can be very useful for the designer when designing new devices.

The subject of this paper is the design and the kinematic analysis of a novel eight-bar elbow joint exoskeleton mechanism that is composed by a motorized Watt I six-bar linkage and a suitable RP dyad, which connects mechanically the external parts of the human arm with the corresponding forearm by hook and loop velcro. Moreover, the human arm is sketched by means of a crossed four-bar linkage, which coupler link is considered as attached to the glyph of the prismatic pair, which is fastened to the forearm.

Therefore, the kinematic analysis of the whole ten-bar mechanism is formulated to investigate the main kinematic performance and for design purposes. The proposed algorithm has given several numerical and graphical results, and finally, a double-parallelogram linkage was considered in combination with the RP dyad and the crossed four-bar linkage by giving a first mechanical design and a 3D-printed prototype.

The main benefits of the proposed eight-bar elbow joint exoskeleton mechanism are:

-

A natural coupling with the human arm;

-

Wearable by workers of different arm sizes;

-

One motor only;

-

A comfortable motor installation under the human arm.

2. Ten-Bar Exoskeleton Elbow Joint Mechanism

The whole one DOF upper-limb exoskeleton mechanism that includes the kinematic sketch of the human arm is represented by the ten-bar mechanism of Figure 1, which consists of the proposed eight-bar elbow joint exoskeleton mechanism and the crossed four-bar linkage. In particular, the first is composed by the Watt I six-bar linkage, which links are numbered by 1 to 6, and the RP dyad of members 6 (coupler), 7 (piston), and 8 (glyph). When the eight-bar elbow joint exoskeleton mechanism is worn, links 1 and 8 are fastened by hook and loop velcro to the arm and forearm, respectively.

The human elbow joint is made up of three bones: the upper arm bone (humerus) and two forearm bones (ulna and radius), which can be sketched by a crossed four-bar linkage of links 1 (arm) and 8 (forearm), along with the crossed links 9 and 10. In fact, the relative motion is not a pure rotation and thus, the upper part of the exoskeleton is fastened to the arm, while the lower part is not rigidly connected to the forearm.

The macroscopic movement of the elbow is actually the result of the interaction between the ends of the bony segments of the arm and forearm in contact. They can be thought of as conjugate surfaces; the relative movement between these two represents the effective motion law of the elbow. If one approaches the movement of the elbow as a plane movement, the projections of these surfaces on it are two curves, which represent the centrodes, whose point of contact is the instantaneous center of rotation. The use of a crossed-four-bar linkage allows to have the position of the instantaneous center of rotation of the coupler link 8 (glyph) close to that of the forearm with respect to the arm.

Applying Grubler’s formula, one has

$$N=3 (n-1)-2l=27-13\cdot 2=1 \mathrm{DOF}$$

(1)

where N, n, and l are the numbers of the degrees of freedom of the rigid links and of the lower kinematic pairs, respectively.

In the following, the kinematic analysis of the human elbow joint and its exoskeleton is formulated.

3. Kinematic Analysis

The kinematic analysis of the one DOF ten-bar mechanism of Figure 2 is developed by first considering separately the Watt I six-bar linkage A₀ABB₀-BCDE and the crossed four-bar linkage M₀MNN₀, respectively, and then joining them at H point to analyze the whole ten-bar mechanism. This chapter is organized in the following three sub-sections:

• Watt I six-bar linkage
• Crossed four-bar linkage
• Ten-bar mechanism

Figure 2. Ten-bar mechanism.

Figure 2. Ten-bar mechanism.

3.1. Watt I Six-Bar Linkage

The main part of the proposed elbow joint exoskeleton mechanism is the Watt I six-bar linkage of Figure 3a, which includes the vector loops of both four-bar linkages A₀ABB₀ and BCDE by giving the following vector equations:

$$\begin{array}{l}{\mathbf{r}}_2+{\mathbf{r}}_{31}-{\mathbf{r}}_1-{\mathbf{r}}_{41}=\mathbf{0}\\ {\mathbf{r}}_{42}+{\mathbf{r}}_5-{\mathbf{r}}_{32}-{\mathbf{r}}_6=\mathbf{0}\end{array}$$

(2)

where vectors r_i are expressed by ${\mathbf{r}}_i=\left(r_i\cos {\theta }_i\right)\mathbf{i}+\left(r_i\sin {\theta }_i\right)\mathbf{j}$ for i = 1, …, 6, where i and j are the unit vectors of the X and Y-axes. The same is for the vectors r₃₁, r₃₂, r₄₁ and r₄₂ which second subscript number refers to loops 1 and 2, respectively.

The ICs (instantaneous centers of rotation) P₃, P₅ and P₆ of the coupler links 3, 5 and 6, respectively, have been determined by applying the Aronhold-Kennedy theorem, according to the graphical constructions of Figure 3b.

Thus, the first of Equation (2) gives

$$\mathcal{A}sin{\theta }_3+\mathcal{B}\cos {\theta }_3+\mathcal{C}=0$$

(3)

which can be solved as follows

$${\theta }_{ 3}=2ta{n}^{-1}{\displaystyle \frac{-\mathcal{A}+\sigma \sqrt{\mathcal{A}{ }^2-{\mathcal{C}}^{ 2}+{\mathcal{B}}^{ 2}}}{\mathcal{C}-\mathcal{B}}}$$

(4)

where σ is equal to ±1 according to the assembly mode.

The coefficients $\mathcal{A}$, $\mathcal{B}$ and $\mathcal{C}$ are obtained as function of the driving angle θ₂ by

$$\begin{array}{l}\mathcal{A}=2 r_2 r_{31}\sin {\theta }_2\\ \mathcal{B}=2 r_{31}\left(r_2\cos {\theta }_2-r_1\right)\\ \mathcal{C}=r_1^2+r_2^2+r_{31}^2-r_{41}^2-2 \hspace{0.17em}{r}_1 r_2\cos {\theta }_2\end{array}$$

(5)

Moreover, solving the first of Equation (2) with respect to θ₄, one has

$${\theta }_4=\tan {\hspace{0.17em}}^{-1}\hspace{0.17em}{\displaystyle \frac{r_{31}\sin {\theta }_3+r_2\sin {\theta }_2}{r_2\cos {\theta }_2+r_{31}\cos {\theta }_3-r_1}}$$

(6)

From the first of Equation (2), the angular velocities ω₃ and ω₄ can be obtained as follows

$$\begin{array}{l}{\omega }_{ 4}={\displaystyle \frac{r_2\sin \left({\theta }_2-{\theta }_3\right)}{r_{41}\sin \left({\theta }_4-{\theta }_3\right)}}{\omega }_{ 2}\\ {\omega }_{ 3}={\displaystyle \frac{r_2\sin \left({\theta }_2-{\theta }_4\right)}{r_{31}\sin \left({\theta }_4-{\theta }_3\right)}}{\omega }_{ 2}\end{array}$$

(7)

where the angles θ₃ and θ₄ are given by Equations (4) and (6), respectively.

Similarly, from the second of Equation (2), one has

$${\theta }_6=2ta{n}^{-1}{\displaystyle \frac{-\mathcal{D}+\sigma \sqrt{\mathcal{D}{ }^2-{\mathcal{F}}^{ 2}+{\mathcal{E}}^{ 2}}}{\mathcal{F}-\mathcal{E}}}$$

(8)

which the coefficients $\mathcal{D}$, $\mathcal{E}$ and $\mathcal{F}$ are given by

$$\begin{array}{c}\mathcal{D}=2 r_{32} r_6\sin {\theta }_3-2 r_{42} r_6\sin {\theta }_4\\ \mathcal{E}=2 r_{32} r_6\cos {\theta }_3-2\hspace{0.17em}{r}_{42} r_6\cos {\theta }_4\\ \mathcal{F}=r_{42}^2+r_{32}^2+r_6^2-r_5^2-2 r_{42} r_{32}\cos {\theta }_3\cos {\theta }_4-2 r_{42} r_{32}\sin {\theta }_3\sin {\theta }_4\end{array}$$

(9)

Thus, solving with respect to θ₅, one has

$${\theta }_{ 5}={\tan }^{-1}\hspace{0.17em}\hspace{0.17em}{\displaystyle \frac{r_{32}\sin {\theta }_3+r_6\sin {\theta }_6-r_{42}\sin {\theta }_4}{r_{32}\cos {\theta }_3+r_6\cos {\theta }_6-r_{42}\cos {\theta }_4}}$$

(10)

From the second of Equation (2), the angular velocities ω₅ and ω₆ are obtained as follows

$${\omega }_{ 5}={\displaystyle \frac{{\omega }_3 r_{32}\sin \left({\theta }_6-{\theta }_3\right)-{\omega }_4 r_{42}\sin \left({\theta }_6-{\theta }_4\right)}{r_5\sin \left({\theta }_6-{\theta }_5\right)}}$$

(11)

$${\omega }_{ 6}={\displaystyle \frac{{\omega }_3 r_{32}\sin \left({\theta }_5-{\theta }_3\right)-{\omega }_4 r_{42}\sin \left({\theta }_5-{\theta }_4\right)}{r_6\sin \left({\theta }_6-{\theta }_5\right)}}$$

(12)

The velocity vectors v_A, v_B, v_C, v_D and v_E of points A, B, C, D and E, respectively, are obtained by assuming the following in vector forms:

$$\begin{array}{l}{\mathbf{v}}_A={\omega }_{ 2}{\left[\begin{array}{cc}-r_2\hspace{0.17em}\sin {\theta }_2,& r_2\hspace{0.17em}\cos {\theta }_2\end{array}\right]}^T\\ {\mathbf{v}}_B={\omega }_{ 4}{\left[\begin{array}{cc}-r_4\hspace{0.17em}\sin {\theta }_4,& r_4\hspace{0.17em}\cos {\theta }_4\end{array}\right]}^T\\ {\mathbf{v}}_C={\left[\begin{array}{cc}{v}_{BX}-r_{32}\hspace{0.17em}{\omega }_3\sin {\theta }_3,& v_{BY}+r_{32}\hspace{0.17em}{\omega }_3\cos {\theta }_3\end{array}\right]}^T\\ {\mathbf{v}}_D={\left[\begin{array}{cc}{v}_{CX}-r_6\hspace{0.17em}{\omega }_6\sin {\theta }_6,& v_{CY}+r_6\hspace{0.17em}{\omega }_6\cos {\theta }_6\end{array}\right]}^T\\ {\mathbf{v}}_E={\left[\begin{array}{cc}{v}_{BX}-r_{42}\hspace{0.17em}{\omega }_4\sin {\theta }_4,& v_{BY}+r_{42}\hspace{0.17em}{\omega }_4\cos {\theta }_4\end{array}\right]}^T\end{array}$$

(13)

where T indicates the transpose matrix.

Finally, the velocity vector v_H6 of the point H, as belonging to the coupler link 6, is given by

$${\mathbf{v}}_{H6}={\left[\begin{array}{cc}{v}_{CX}+{\omega }_6\left(d_1+d_3\right)\hspace{0.17em}\sin {\theta }_6-{\omega }_6 d_2\cos {\theta }_6,& v_{CY}-{\omega }_6\left(d_1+d_3\right)\hspace{0.17em}\cos {\theta }_6-{\omega }_6 d_2\sin {\theta }_6\end{array}\right]}^T$$

(14)

3.2. Crossed Four-Bar Linkage

The crossed four-bar linkage of Figure 4a, which includes the corresponding vector loop of the linkage M₀MNN₀, sketches the human elbow joint, while Figure 4b shows the graphical construction for determining the ICs of each link.

Therefore, the following vector-loop equation is obtained

$${\mathbf{r}}_{10}+{\mathbf{r}}_8-{\mathbf{r}}_9-{\mathbf{r}}_{11}=0$$

(15)

where ${\mathbf{r}}_i=\left(r_i\cos {\theta }_i\right)\mathbf{i}+\left(r_i\sin {\theta }_i\right)\mathbf{j}$ for i = 8, …, 11.

Thus, one has

$$\mathcal{G}\sin {\theta }_8+\mathcal{H}\cos {\theta }_8+\mathcal{I}=0$$

(16)

which can be solved by giving

$${\theta }_8=2{\tan }^{-1}{\displaystyle \frac{-\mathcal{G}+\sigma \sqrt{\mathcal{G}{ }^2-{\mathcal{I}}^{ 2}+{\mathcal{H}}^{ 2}}}{\mathcal{I}-\mathcal{H}}}$$

(17)

where σ is equal to ±1 according to the assembly mode.

The coefficients $\mathcal{G}$, $\mathcal{H}$ and $\mathcal{I}$ are given as function of the driving crank angle θ₁₀ by

$$\begin{array}{c}\mathcal{G}=2 r_{10} r_8\sin {\theta }_{10}\\ \mathcal{H}=2 r_8\left(r_{10}\cos {\theta }_{10}-r_{11}\right)\\ \mathcal{I}=r_{11}^2+r_{10}^2+r_8^2-r_9^2-2 \hspace{0.17em}{r}_{10}\hspace{0.17em}{r}_{11}\cos {\theta }_{10}\end{array}$$

(18)

Moreover, Equation (15) can be solved with respect to θ₉ by giving

$${\theta }_{ 9}={\tan }^{-1}{\displaystyle \frac{r_{11}\sin {\theta }_{11}+r_8\sin {\theta }_8-r_{10}\sin {\theta }_{10}}{r_{11}\cos {\theta }_{11}+r_8\cos {\theta }_8-r_{10}\cos {\theta }_{10}}}$$

(19)

From the Equation (15), the angular velocities ω₈ and ω₉ are obtained as follows

$$\begin{array}{l}{\omega }_{ 8}={\displaystyle \frac{r_{10}\sin \left({\theta }_{10}-{\theta }_9\right)}{r_8\sin \left({\theta }_9-{\theta }_8\right)}}{\omega }_{ 10}\\ {\omega }_{ 9}={\displaystyle \frac{r_{10}\sin \left({\theta }_{10}-{\theta }_8\right)}{r_9\sin \left({\theta }_9-{\theta }_8\right)}}{\omega }_{ 10}\end{array}$$

(20)

The velocity vectors of points M and N are given by

$$\begin{array}{c}{\mathbf{v}}_M={\omega }_{10}{\left[\begin{array}{cc}-r_{10}\hspace{0.17em}\sin {\theta }_{10},& r_{10}\hspace{0.17em}\cos {\theta }_{10}\end{array}\right]}^T\\ {\mathbf{v}}_N={\omega }_9{\left[\begin{array}{cc}-r_9\hspace{0.17em}\sin {\theta }_9,& r_9\hspace{0.17em}\cos {\theta }_9\end{array}\right]}^T\end{array}$$

(21)

3.3. Ten-Bar Mechanism

The formulation that has been developed in the previous two sub-sections is now combined in order to obtain a general algorithm for the kinematic analysis of the whole ten-bar mechanism. Additional kinematic considerations are applied by using the Aronhold-Kennedy theorem, as shown in Figure 5. In particular, the ICs P₆, P₈, and P₆₈ are of interest in order to express the velocity vectors v_H6 and v_H8 of point H as belonging to the coupler links 6 and 8, respectively, along with their relative velocity vector v_H68.

Thus, one has

$${\mathbf{v}}_{H6}=v_{H8}+v_{H68}$$

(22)

where each velocity vector is given by

$$\begin{array}{l}{\mathbf{v}}_{H8}={\omega }_{ 8}\times P_{\hspace{0.17em}8} H\\ {\mathbf{v}}_{H6}={\omega }_{ 6}\times P_{\hspace{0.17em}6} H\\ {\mathbf{v}}_{H68}={\omega }_{ 68}\times P_{\hspace{0.17em}68} H\end{array}$$

(23)

Therefore, in scalar form, one has

$${\omega }_6\hspace{0.17em}{P}_6{P}_{68}=\hspace{0.33em}{\omega }_8\hspace{0.17em}{P}_8{P}_{68}$$

(24)

where $P_6{P}_{68}$ and $P_8{P}_{68}$ are the distances of the ICs P₆ and P₈ with respect to P₆₈.

The angular velocity ${\omega }_8$ of the coupler link 8 of the four-bar linkage is now related to that of the coupler link 6 of the Watt I six-bar linkage by means of the ICs P₆, P₈ and P₆₈.

4. Graphical and Numerical Results

The proposed formulation for the kinematic analysis of the ten-bar mechanism, which includes both the eight-bar elbow joint exoskeleton mechanism and the human elbow joint mechanism, has been implemented in Matlab for validation purposes.

In fact, Figure 6 and Figure 7 show the results for the crank angles θ₂ = 255° and θ₂ = 290° by giving the angular velocities of all moving links and the linear velocities of points A, B, C, D, E, H, M and N. The geometric input data are reported in

Table 1. The geometric input data in the case of Figure 6 and Figure 7.

r1 [mm]	r2 = r6 [mm]	r31 [mm]	r32 [mm]	r41 [mm]	r42 [mm]
70	30	45	50	65	40
r8 [mm]	r9 [mm]	r10 [mm]	r11 [mm]	d1 = d3 [mm]	d2 [mm]
25	65	60	18	30	117.50

, where the link lengths of the Watt I six-bar linkage, have been chosen in such a way to be compatible with the application as elbow joint exoskeleton mechanism and with the aim to validate, in general, the proposed kinematic analysis algorithm.

The results of the proposed algorithm for the input data of Table 1 and the driving angular velocity ω₂ = 1 rad/s, are reported in

Table 2. Output linear velocities of all significant points for the case of Figure 6 and Figure 7.

θ2 [deg]	vA [mm/s]	vB [mm/s]	vC [mm/s]	vD [mm/s]	vE [mm/s]
255	[28.978, −7.765]T	[23.220, −17.463]T	[16.82, −28.239]T	[34.78, −35.324]T	[37.509, −28.21]T
290	[28.191, 10.261]T	[12.906, −5.905]T	[−4.077, −23.86]T	[13.328, −23.80]T	[20.848, −9.538]T
	vH6 [mm/s]	vH8 [mm/s]	vH68 [mm/s]	vM [mm/s]	vN [mm/s]
255	[8.648, 56.278]T	[34.933, 39.356]T	[−26.38, 16.937]T	[8.853, 8.549]T	[17.782, 2.818]T
290	[−39.128, 44.18]T	[16.092, 24.658]T	[−54.675, 20.00]T	[5.443, 6.483]T	[12.502, 3.904]T

and

Table 3. Output angular velocities of all moving links for the case of Figure 6 and Figure 7.

θ2 [deg]	ω3 [rad/s]	ω4 [rad/s]	ω5 [rad/s]	ω6 [rad/s]	ω8 [rad/s]	ω9 [rad/s]	ω10 [rad/s]	ω11 [rad/s]
255	−0.251	0.447	−0.127	0.644	0.424	0.277	0.205	0.219
290	−0.4944	0.2183	−0.2688	0.5802	0.3007	0.2015	0.1411	0.2795

.

5. Application and Prototype

The proposed general formulation for the kinematic analysis of the ten-bar mechanism of Figure 2 can be used to analyze and design a suitable eight-bar elbow joint exoskeleton mechanism of different shapes and sizes. In particular, the case of when the Watt I six-bar linkage becomes a double-parallelogram linkage and the crossed four-bar linkage becomes an anti-parallelogram linkage is now considered, and the whole mechanism takes the shape of Figure 8a, according to the application that is sketched in Figure 8b, which also shows both lengths a and b of the lower and upper human arms.

According to what was reported in [36], the mean values of a = 241 mm and b = 338 mm have been assumed, where each of them has been calculated as the arithmetic mean between the maximum and minimum lengths of the lower and upper arms for males and females, respectively. Moreover, the proposed exoskeleton is supposed to be worn at about half lengths of a and b for the lower and upper arms.

The geometric input data of

Table 4. The geometric input data in the case of Figure 9 and Figure 10.

r1 = r31 = r32 = r5 = d [mm]	r2 = r41 = r42 = r6 = c = e [mm]	r8 = r11 [mm]	r9 = r10 [mm]	d1 = d3 [mm]	d2 [mm]
70	60	18	57.90	30	117.50

have been chosen along with the input angular velocity ω₂ = 1 rad/s, and thus, running the same Matlab program, the results of Figure 9 and Figure 10 have been obtained for the crank angles θ₂ = 300° and θ₂ = 252°, respectively.

In particular, a and b are only related to the lower (6) and upper (1) arm supports of the proposed exoskeleton mechanism, where a is about the double of d₂.

Moreover, this design permits the wearability by different workers or persons of average sizes, thanks to the specific characteristic of auto-adaptability, which is given by the piston-glyph pair. The obtained results are reported in

Table 5. Output linear velocities of all significant points for the case of Figure 9 and Figure 10.

θ2 [deg]	vA = vB = vC [mm/s]			vD = vE [mm/s]
300	[51.962, 30.000]T			[112.583, 65.000]T
252	[57.063, −18.5410]T			[13.328, −23.804]T
	vH6 [mm/s]	vH8 [mm/s]	vH68 [mm/s]	vM [mm/s]	vN [mm/s]
300	[−58.750, 101.758]T	[−45.816, 103.288]T	[−13.556, −11.892]T	[9.158, 29.955]T	[29.650, 47.93]T
252	[36.309, 111.749]T	[58.722, 103.305]T	[−22.609, 8.507]T	[16.74, 19.605]T	[35.108, 12.69]T

and

Table 6. Output angular velocities of all moving links for the case of Figure 9 and Figure 10.

θ2 [deg]	ω3 = ω5 [rad/s]	ω4 = ω6 [rad/s]	ω8 [rad/s]	ω9 [rad/s]	ω10 [rad/s]	ω11 [rad/s]
300	0	1	1.514	0.973	0.541	−0.514
252	−0.4944	0.2183	1.0901	0.6448	0.4453	−0.0901

. The mechanical design of the proposed ten-bar mechanism has been developed in order to build and test under a kinematic point of view the first 3D-printed planar prototype of Figure 11, which shows a step-by-step sequence of the closing motion in comparison with the corresponding Matlab graphical results. Similarly, the whole sequence is shown in Figure 12.

6. Conclusions

A novel eight-bar elbow joint exoskeleton mechanism, which consists of a motorized Watt I six-bar linkage and a suitable RP dyad, has been proposed, and a suitable algorithm for the kinematic analysis of the whole one DOF ten-bar mechanism that includes the human elbow joint mechanism has been formulated for designing elbow joint exoskeleton mechanisms of different shapes and sizes. A first planar prototype has been designed and built by means of a 3D printer by considering the mean lengths of a = 241 mm and b = 338 mm of the lower and upper arms, respectively, and for males and females, and supposing to wear the proposed exoskeleton at about half lengths of them. Moreover, this design permits the wearability by different workers or persons of average sizes, thanks to the specific characteristic of auto-adaptability, while the corresponding algorithm allows to change the link sizes for analyzing the kinematic performance in different conditions and configurations. The dynamic analysis in load conditions of the proposed exoskeleton closing motion, along with the actuation and control, will be part of the next developments.