The 14th IFToMM World Congress, Taipei, Taiwan, October 25-30, 2015
DOI Number: 10.6567/IFToMM.14TH.WC.OS13.131
Mass equivalent triads
V. van der Wijk∗
King’s College London, Centre for Robotics Research, London, United Kingdom
Abstract—In this paper it is shown how a general 3-DoF
triad can be designed mass equivalent to a general (1-DoF) link element. This is useful in the synthesis of shaking force balanced and statically balanced mechanisms, for instance to add or remove a number of DoFs of a balanced mech-anism maintaining its balance. Also it can be used as a simple approach for synthesis of complex balanced mech-anisms. To obtain the parameters for mass equivalence, a mass equivalent model with real and virtual equivalent masses is used. The characteristics of this model are ex-plained and the properties of a mass equivalent triad are shown. Subsequently the parameters of a mass equivalent triad are derived with the method of rotations about the principal points (RAPP) and application examples are il-lustrated and discussed.
Keywords: mass equivalent modeling, shaking force balance, static balance, mass equivalent triad, principal vector linkage
I. Introduction
Figure 1a shows a mechanism link with two joints Aiand
Ai+1 and a center of mass (CoM) in Si, which is a point
defined by parameters ei and fi as illustrated. The mass
of such a general element cannot be modeled mass equiva-lently with common mass modeling methods such as those in [8] [2]. This is since these methods only use equivalent
masses in the joints, here Ai and Ai+1, which means that
only a CoM that is located on the line through the joints
can be modeled. A nonzero value of fi in Fig. 1a then is
not possible.
In [3] a new mass equivalent model of the link in Fig. 1a was proposed and validated, which is shown in Fig. 1b.
Here a real equivalent mass ma
i is located in Ai, a real
equivalent mass mb
i is located in Ai+1, and a virtual
equiv-alent mass mci is located in both Ji1 and Ji2. Ji1 is
lo-cated at a distance si1 =
√
e2
i + fi2from Sinormal to the
line AiSi, as illustrated, and Ji2 is located at a distance
si2=
√
(li− ei)2+ fi2from Sinormal to the line Ai+1Si,
as illustrated. As in Fig. 1a Siis the CoM of the four
equiv-alent masses.
In [3] [4] it was shown how with this model the motion of the mass of a general closed kinematic chain can be an-alyzed as an open chain where one of the elements is con-sidered with equivalent masses. With this method it was possible to synthesize general inherently shaking force bal-anced closed-chain linkages which are statically balbal-anced
∗v.vanderwijk@kineticart.nl
as well. In [5] it was shown that this mass equivalent model can represent not only the mass of a general single element, but also the mass of multi-DoF linkages. For all motion these multi-DoF linkages then are mass equivalent to the model in Fig. 1b, which was shown and explained by the synthesis of a mass equivalent 2-DoF dyad linkage. The aim of this paper is to extend this theory to the synthesis of mass equivalent 3-DoF triad linkages. This step requires the use of principal vectors for calculating the linkage parame-ters, which for the 2-DoF dyad linkage could be omitted by using a simpler analysis method.
The application of mass equivalent linkages was shown in a preliminary study presented in [6] and in [5] where mass equivalent linkages were applied to add DoFs to a shaking force balanced or statically balanced mechanism, maintaining its balance. A balanced 3-DoF parallel manip-ulator was synthesized from a 0-DoF structure. At the end of this paper application examples of mass equivalent triads are shown and discussed. For a realistic interpretation, all illustrations in this paper are drawn to scale.
Si fi ei li Ai Ai+1 qi mi ~ (b) (a) Si fi ei li Ai Ai+1 qi mai mbi Ji1 Ji2 mc i mc i Si f* i e* i l* i Ai Ai+1 qi mai mb i Ji1 Ji2 mc i mc i (c) ~ si1 si2 si1 * si2 *
Fig. 1. a) Link element with two joints Aiand Ai+1and a general CoM
Si; b) Mass equivalent model of the link element with a real equivalent mass mai in Ai, a real equivalent mass mbiin Ai+1, and a virtual equiv-alent mass mciin both Ji1and Ji2; c) mai, mbi, and mciare independent of the scale of the link.
II. Mass equivalent triad
The conditions for which the model in Fig. 1b is mass
equivalent with the link element in Fig. 1a are ma
iei =
mb
i(li − ei) and mcili = (mai + mbi)fi, which define the
CoM of the model in Si, and mai + m
b
i = mi which is
the total mass of the model equal to the mass of the link.
Since mass mci = mifi/liis not part of the ’real’ mass of
the link, this mass is referred to as a virtual equivalent mass
while masses ma
i = mi(1− ei/li) and mbi = miei/li are
referred to as the real equivalent masses [3].
In Fig. 1c it is shown that when the model is scaled, the equivalent masses remain unchanged. The values of the equivalent masses are independent of the size of the
model. They can be described by ma
i = mi(1 − λ1),
mbi = miλ1, and mci = miλ2with the constants λ1= ei/li
and λ2= fi/li. Si li Ai Ai+1 (a) (b) fi2 fi1 mi1 fi3 mi3 li1 li2 li3 ei2 ei1 B1 B2 ei3 mi2 Si Ai Ai+1 l*i mi3 mi1 mi2 B1 B2 fi1 ei1 ei2 fi2 ei3 fi3
Fig. 2. Triad that is mass equivalent with the link element in Fig. 1a in two poses (drawn to scale with parameters λ1 = 0.5991, λ2= 0.2658,
li2/li1 = 1.5540, li3/li1 = 1.2423, mi2/mi1 = 0.8947, and
mi3/mi1= 1.2632).
While the length of the rigid link in Fig. 1a is fixed, a
released length l∗i as in Fig. 1c can be obtained for instance
as the distance between the extremities of a triad. Figure 2 shows a triad with link lengths li1, li2, and li3 where l∗i is
the distance between joints A1 and Ai+1. Since the link
masses mi1, mi2, and mi3are located such that their
com-mon CoM is exactly in Si of the model in Fig. 1c for any
of its poses and mi1+ mi2+ mi3 = mi, this triad is mass
equivalent to the link in Fig. 1a. Practically this could mean that in a balanced linkage a general single link element can be substituted with a mass equivalent triad without affect-ing the balance. Alternatively it could mean that the mass motion of the triad can be represented by the mass motion of a single link element.
III. Method of rotations about the principal points (RAPP)
The design parameters of the triad for mass equivalence can be calculated with the method of rotations about the
principal points (RAPP) [3][5]. Figure 3 shows the triad in
Fig. 2 with a graphical construction of parallelograms. This construction is known as a (3-DoF) principal vector
link-age with which the motion of masses mi1, mi2, and mi3is
traced with respect to their common CoM in Si[3]. Of this
principal vector linkage links AiB1, B1B2, and B2Ai+1
are the principal elements and P1, P2, and P3are the
prin-cipal points in each prinprin-cipal element.
Si li Ai Ai+1 (a) (b) mi1 mi3 li1 li2 l i3 B1 B2 mi2 Si Ai Ai+1 l*i mi3 mi1 mi2 P3 P1 P2 a1 p1 a3 p3 a23 a21 a1 p1 a3 p3 a23 a21 a1 c1 b1 P1 B1 Ai P3 B2 a3 c3 b3 Ai+1 B1 B2 a21 c2 b21 P2 B2 B1 a23 b23 pa 2 pb 2 P1 P2 P3
Fig. 3. Mass equivalent triad with principal points P1, P2, and P3and its principal vector linkage which traces the common CoM of mi1, mi2, and
mi3in Sifor all motion of the linkage, drawn for two poses.
The principal points are defined within each element with the principal dimensions a1, a21, a23and a3, which are the lengths of the sides of the illustrated parallelograms. Then
P1is located at an a1distance from B1along the line trough
B1and mi1and this point is defined relative to line B1Ai
with parameters b1and c1. Similarly P3is located at an a3
distance from B2along the line trough B2and mi3and this
point is defined relative to line B2Ai+1with parameters b3
and c3. P2 is located at an a21 distance from B1 and an
a23distance from B2. This point is defined relative to line
B1B2with parameters b21 from B1and c2 relative to line
B1B2, as illustrated.
The parallelograms trace the common CoM in Si for all
motion for the balance conditions [3]
mi1p1= (mi2+ mi3)a1, mi1a21= mi2pa2 (1)
mi3p3= (mi1+ mi2)a3, mi3a23= mi2pb2
aligned with B1P2 and B2P2. Because of similarity, the mass parameters of each outer principal element are related as p1+ a1 a1 = ei1 b1 =fi1 c1 (2) p3+ a3 a3 = ei3 b3 =fi3 c3
The mass parameters of elements 1 and 3 then can be
de-rived to depend on biand cias
ei1 = ( p1 a1 + 1)b1= ( mi2+ mi3 mi1 + 1)b1 fi1 = ( p1 a1 + 1)c1= ( mi2+ mi3 mi1 + 1)c1 (3) ei3 = ( p3 a3 + 1)b3= ( mi1+ mi2 mi3 + 1)b3 fi3 = ( p3 a3 + 1)c3= ( mi1+ mi2 mi3 + 1)c3
For element 2 the CoM can be described based on P2as [3]
ei2 = − mi3li2 mi2 + (mi1+ mi3 mi2 + 1)b21 (4) fi2 = ( mi1+ mi3 mi2 + 1)c2
which can be interpreted as that the location of P2in
ele-ment 2 is found as the common CoM of mi1 projected in
B1, mi3projected in B2, and mi2at its actual location.
S
il
iA
iA
i+1l
i1l
i2l
i3B
1B
2P
3P
1P
2a
1a
3a
23a
21m
aim
b im
c im
c im
c im
cim
cim
ciFig. 4. Mass equivalent model of the triad with the projection of the real equivalent mass maiin Ai, the real equivalent mass mbiin Ai+1, and the virtual equivalent mass mc
itwice about each principal point as illustrated.
To calculate the parameters of the principal points biand
ci, Fig. 4 shows the mass equivalent model of the triad. The
real equivalent masses ma
i and mbi are located in joints Ai
and Ai+1, respectively, and the virtual equivalent mass mci
is located twice about each principal point P1, P2, and P3
as illustrated. This projection is explained in [3], and is for each element of similar composition as the models in Fig. 1b.
The model in Fig. 4 is analyzed with the linear momen-tum equations of the three relative motions of the principal
Si Ai Ai+1 li2 B1 B2 P2 a 23 a 21 ma i mb i mci m c i Si Ai Ai+1 l i3 B1 B2 P3 a 3 mai mb i mc i mci q i2 . xi3 yi3 q i3 . Si Ai Ai+1 l i1 B1 P1 a 1 ma i mb i mc i mc i q i1 . xi1 yi1 (a) B2 (b) (c) xi2 y i2
Fig. 5. a) Relative motion of DoF 1 with rotational motion about P1; b) Relative motion of DoF 2 with rotational motion about P2; c) Relative motion of DoF 3 with rotational motion about P3.
vector linkage, which are the rotational motions about each
principal point P1, P2, and P3individually. An important
property of a virtual equivalent mass is that its mass acts as a real mass for rotational motion while is has zero mass for translational motion of its element [3]. This is since the vir-tual equivalent masses represent solely the rotational mass motion of an element, while translational mass motion of an element is represented solely with real equivalent masses.
In Fig. 5 the relative motions are illustrated. Figure 5a
shows the relative motion of DoF 1 where element AiB1
rotates about P1 and elements B1B2 and B2Ai+1 solely
translate. For this motion the virtual equivalent masses in
element AiB1act as a real mass while the virtual equivalent
masses in elements B1B2and B2Ai+1are zero. Figure 5b
shows the relative motion of DoF 2 where element B1B2
rotates about P2 and elements AiB1 and B2Ai+1 solely
element B1B2act as a real mass while the virtual equivalent
masses in elements AiB1and B2Ai+1 are zero. Figure 5c
shows the relative motion of DoF 3 where element B2Ai+1
rotates about P3and elements AiB1and B1B2solely
trans-late. For this motion the virtual equivalent masses in
ele-ment B2Ai+1act as a real mass while the virtual equivalent
masses in elements AiB1and B1B2are zero.
Ai B1 ma i mc i mci (a) mb i li1 a 1 b1 c 1 l i2 B1 B2 P2 a23 a21 ma i mb i mc i mc i b21 c 2 Ai+1 l i3 B2 P3 a3 ma i mb i mci mc i b3 c3 (b) (c) xi3 yi3 xi1 yi1 xi2 y i2
Fig. 6. Reduced mass models of (a) DoF 1 where P1 is the common CoM, (b) DoF 2 where P2is the common CoM, and (c) DoF 3 where P3 is the common CoM. For rotational motion about the principal points the linear momentum of these models is equal to the linear momentum of the respective relative motion in Fig. 5.
The linear momentum of the relative motions in Fig. 5 can be represented with the reduced mass models in Fig. 6.
For rotational motion about P1of the model in Fig. 6a the
linear momentum equations with respect to reference frame
xi1yi1 are equal to the linear momentum equations of the
motion in Fig. 5a. For rotational motion about P2 of the
reduced mass model in Fig. 6b the linear momentum
equa-tions with respect to reference frame xi2yi2are equal to the
linear momentum equations of the motion in Fig. 5b. For
rotational motion about P3of the model in Fig. 6c the
lin-ear momentum equations with respect to reference frame
xi3yi3 are equal to the linear momentum equations of the
motion in Fig. 5c. Therefore these models are also named Equivalent Linear Momentum Systems (ELMS) [3]. As a
result, the principal points P1, P2, and P3are the common
CoMs of the reduced mass models. Therefore the parame-ters in each reduced mass model are related by
mai(li1− b1) = mbib1, mcili1= (mai + m b i)c1 maib21= mbi(li2− b21), mcili2= (mai + mbi)c2 (5) maib3= mbi(li3− b3), mcili3= (mai + m b i)c3 From these equations b1, c1, b21, c2, b3, and c3are derived as b1= ma ili1 ma i+m b i = (1− λ1)li1, c1= mc ili1 ma i+m b i = λ2li1 b21= mb ili2 ma i+m b i = λ1li2, c2= mc ili2 ma i+m b i = λ2li2 (6) b3= mb ili3 ma i+m b i = λ1li3, c3= mc ili3 ma i+m b i = λ2li3
Subsequently with (3) and (4) parameters ei1, fi1, ei2, fi2,
ei3, and fi3 are obtained with which the principal
dimen-sions a1, a21, a23, and a3can be calculated as
a1 = √ b2 1+ c21= li1 √ (1− λ1)2+ λ22 a21 = √ b2 21+ c22= li2 √ λ2 1+ λ22 (7) a23 = √ (li2− b21)2+ c22= li2 √ (1− λ1)2+ λ22 a3 = √ b2 3+ c23= li3 √ λ2 1+ λ22
With (1) then p1, pa2, pb2, and p3are calculated as
p1= mi2+ mi3 mi1 a1, p3= mi1+ mi2 mi3 a3 (8) pa2= mi1 mi2 a21, pb2= mi3 mi2 a23
Substituting these parameters in (3) and (4) with mai+mbi =
mi1+ mi2+ mi3then leads to ei1= mal i1 mi1 , fi1= mcl i1 mi1 (9) ei2= mbl i2− mi3li2 mi2 , fi2= mcl i2 mi2 ei3= mbl i3 mi3 , fi3= mcl i3 mi3
where the mass parameters of the triad are dependent on the equivalent masses.
IV. Discussion
The method of rotations about the principal points gives fundamental insight. The principal points in the reduced mass models in Fig. 6 are related with the so called ’barycenters’ in [7]. Contrary to the barycenters that are obtained without understanding, the principal points have physical meaning as being the joints of a principal vec-tor linkage with principal dimensions, as shown in Fig. 3. Therefore this method may be valuable also for general dy-namical analysis. It is interesting to note that the reduced mass models are of similar composition as the mass equiv-alent models in Figs. 1b and 1c.
For the calculation of the principal points in the elements at the extremities, here elements 1 and 3, it is also possible to use the method of rotations about the principal joints
as shown in [3] [5]. Then the results for P1 and P3 are
obtained quicker and show to be exactly equal to the results for the principal points of a mass equivalent dyad.
The mass equivalent triad in Fig. 2 can be regarded a
general force balanced 4R four-bar linkage when joints Ai
and Ai+1are fixed pivots with the base. The common CoM
in Si then is a stationary point in the base. The balance
conditions of this linkage were found in another way in [1]. Figure 7 shows the result of a general force balanced
e3 l 1 l 2 l 3 l4S -o2 -e1 f1 m3 f3 A1 A3 A0 m4 e4 f4 A2 (a) S2 e3 l 3 l4S -o2 -e1 m1 f1 m3 f3 A1 A3 A0 m4 e4 f4 A2 (b) m22 m21 m23 B1 B 2 f22 f21 f23 e21 e23 l 1 o1 o1 m1 S2 f22 f21 m21 f23 m23 l 21 l22 l 23 e22 e21 B1 B2 e23 m22 l* 2 e22
Fig. 7. Force balanced 6R six-bar linkage obtained from a general force balanced 4R four-bar linkage A0A1A2A3with coupler link A1A2 sub-stituted with the mass equivalent triad in Fig. 2, illustrated for two poses.
A1A2is substituted with the mass equivalent triad in Fig. 2.
Since the distance l2 is no longer fixed, two DoFs are
gained, obtaining a force balanced 6R six-bar linkage of which the common CoM is in S for all motion. The mass
parameters of the other links, i.e. the CoMs of m1, m3,
and m4, and the location of the common CoM in S are not
affected by this substitution while force balance is main-tained.
In Fig. 8 it is shown how link A2A3of a general force
balanced 4R four-bar linkage A0A1A2A3 can be
substi-tuted with a mass equivalent triad. For the mass
equiva-lent model of the illustrated triad holds λ1 = 1.5700 and
λ2 = 0.1978. Also here the mass parameters of the other
links are not affected by this substitution while force bal-ance is maintained.
In Figs. 9 and 10 it is shown how the balanced 6R six-bar linkage in Fig. 7, which can also be considered a
bal-m
2f
2e
2l
1l
2l
31l
4S
-o
o
1 2-e
1m
1f
1A
1A
3A
0m
4e
4f
4A
2S
3m
2f
2e
2l
1l
2l
4S
-o
o
1 2-e
1m
1f
1A
1A
3A
0m
4e
4f
4A
2S
3m
31m
31m
32m
32m
33m
33l
33l
32l
31l
33l
32B
1B
2B
1B
2(a)
(b)
Fig. 8. Force balanced 6R six-bar linkage obtained from a general force balanced 4R four-bar linkage A0A1A2A3with link A2A3substituted with a mass equivalent triad, illustrated for two poses.
anced 2-RRR parallel mechanism, can be synthesized from a single mass model. The starting point is the mass model in Fig. 9a, which is equal to the model in Fig. 1a. This model can be divided in two equivalent mass models as il-lustrated in Fig. 9b, where the common CoM of both mod-els is in S and their combined mass is equal to the model in Fig. 9a. By mass equivalent modeling then each of the two mass models can be substituted with a mass equivalent triad as shown in Fig. 9c. As a last step the elements at the extremities can be combined as shown in Fig. 10 where
mp= m13+ m23. The result is a balanced 2-RRR parallel
mechanism of which the common CoM of the moving links is in S for all motion.
S S S1 S2 A0 B0 A0 B0 A3 B3 S1 S2 B0 A1 B1 A2 A 3 B2 B3 m11 m21 m12 m22 m13 m 23 (a) (b) (c) S A0
Fig. 9. a) An initial mass model (b) can be divided in two equivalent mass models (c) which each can be substituted with a mass equivalent triad.
S1 A0 B1 A3 B2 B3 m11 m21 m12 m22 m13 m23 mp S2 A1 A2 B0 S
Fig. 10. A balanced 2-RRR parallel mechanism obtained by combining the links at the extremities of the two mass equivalent triads in Fig. 9c of which the common CoM is in S for all motion.
V. Conclusion
In this paper it was shown how a general 3-DoF triad can be designed mass equivalent to a general (1-DoF) link el-ement. For finding the parameters for mass equivalence, a mass equivalent model with real and virtual equivalent masses was used. First the characteristics of this model were explained and subsequently the properties of a mass equivalent triad were obtained. With the method of rota-tions about the principal points (RAPP) the parameter val-ues of a mass equivalent triad were derived.
As an application example it was shown how a force anced 6R five-bar linkage can be obtained from a force bal-anced 4R four-bar linkage by either substituting the cou-pler link or by substituting the crank or rocker link with a mass equivalent triad. It was also shown how a balanced 2-RRR parallel manipulator can be obtained from a single mass equivalent model by dividing it in two mass equiva-lent models and by substituting each mass equivaequiva-lent model with a mass equivalent triad.
Acknowledgement
This publication was financially supported by the Niels Stensen Fellowship.
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