Many rotating shafts and axles used for power transmission experience torsional vibration, particularly when the prime mover is a reciprocating engine. The shafts used in high‐speed machinery, especially those carrying heavy wheels, are subjected to dynamic torsional forces and vibration. A solid or hollow cylindrical rod of circular section undergoes torsional displacement or twisting such that each transverse section remains in its own plane when a torsional moment is applied. In this case the cross‐sections of the rod do not experience any motion parallel to the axis of the rod. However, if the cross‐section of the rod is not circular, the effect of a twist will be more involved. In this case the twist will be accompanied by a warping of normal cross‐sections. The torsional vibrations of uniform and nonuniform rods with circular cross‐section and rods with noncircular section are considered in this chapter. For noncircular sections, the equations of motion are derived using both the Saint‐Venant and the Timoshenko–Gere theories. The methods of determining the torsional rigidity of noncircular rods are presented using the Prandtl stress function and the Prandtl membrane analogy.
Consider an element of a nonuniform circular shaft between two cross‐sections at x and , as shown in Fig. 10.1(a). Let denote the torque induced in the shaft at x and time t and the torque induced in the shaft at and at the same time t. If the angular displacement of the cross‐section at x is denoted as , the angular displacement of the cross‐section at can be represented as . Let the external torque acting on the shaft per unit length be denoted . The inertia torque acting on the element of the shaft is given by , where is the mass polar moment of inertia of the shaft per unit length. Noting that and , Newton's second law of motion can be applied to the element of the shaft to obtain the equation of motion as
From the strength of materials, the relationship between the torque in the shaft and the angular displacement is given by [1]
where G is the shear modulus and is the polar moment of inertia of the cross‐section of the shaft. Using Eq. (10.2), the equation of motion, Eq. (10.1), can be expressed as
The equation of motion of a nonuniform shaft, using the variational approach, has been derived in Section 4.11.1. In this section the variational approach is used to derive the equation of motion and the boundary conditions for a nonuniform shaft with torsional springs (with stiffnesses and ) and masses (with mass moments of inertia and ) attached at each end as shown in Fig. 10.1.
The cross‐sections of the shaft are assumed to remain plane before and after angular deformation. Since the cross‐section of the shaft at x undergoes an angular displacement about the center of twist, the shape of the cross‐section does not change. The cross‐section simply rotates about the x axis. A typical point P rotates around the x axis by a small angle as shown in Fig. 10.2. The displacements of point P parallel to the y and z axes are given by the projections of the displacement PP′ on oy and oz:
Since is small, we can write
so that
Thus, the displacement components of the shaft parallel to the three coordinate axes can be expressed as
The strains in the shaft are assumed to be
and the corresponding stresses are given by
The strain energy of the shaft and the torsional springs is given by
where . The kinetic energy of the shaft can be expressed as
The work done by the external torque can be represented as
The application of the generalized Hamilton's principle yields
or
The variations in Eq. (10.13) can be evaluated using integration by parts to obtain
Note that integration by parts with respect to time, along with the fact that at and , has been used in deriving Eqs. (10.16) and (10.17). By using Eqs. (10.14)– (10.17) in Eq. (10.13), we obtain
By setting the two expressions under the braces in each term of Eq. (10.18) equal to zero, we obtain the equation of motion for the torsional vibration of the shaft as
where is the mass moment of inertia of the shaft per unit length, and the boundary conditions as
Each of the equations in (10.20) can be satisfied in two ways but will be satisfied only one way for any specific end conditions of the shaft. The boundary conditions implied by Eqs. (10.20) are as follows. At , either is specified (so that ) or
At , either is specified (so that ) or
In the present case, the second conditions stated in each of Eqs. (10.21) and (10.22) are valid.
For a uniform shaft, Eq. (10.19) reduces to
By setting , we obtain the free vibration equation
where
It can be observed that Eqs. (10.23)–(10.25) are similar to the equations derived in the cases of transverse vibration of a string and longitudinal vibration of a bar. For a uniform shaft, and Eq. (10.25) takes the form
By assuming the solution as
Eq. (10.24) can be written as two separate equations:
The solutions of Eqs. (10.28) and (10.29) can be expressed as
where A, B, C, and D are constants. If denotes the nth frequency of vibration and the corresponding mode shape, the general free vibration solution of Eq. (10.24) is given by
The constraints and can be evaluated from the initial conditions, and the constraints and can be determined (not the absolute values, only their relative values) from the boundary conditions of the shaft. The initial conditions are usually stated in terms of the initial angular displacement and angular velocity distributions of the shaft.
For a uniform circular shaft of length l fixed at both ends, the boundary conditions are given by
The free vibration solution is given by Eq. (10.27):
Equations (10.33) and (10.35) yield
and the solution can be expressed as
where C′ and D′ are new constants. The use of Eq. (10.34) in (10.37) gives the frequency equation
The natural frequencies of vibration are given by the roots of Eq. (10.38) as
or
The mode shape corresponding to the natural frequency can be expressed as
The free vibration solution of the fixed–fixed shaft is given by a linear combination of its normal modes:
Since the torque, , is zero at a free end, the boundary conditions of a free–free shaft are given by
In view of Eq. (10.27), Eqs. (10.42) and (10.43) can be expressed as
Eq. (10.30) gives
Eqs. (10.44) and (10.47) yield
and Eqs. (10.45) and (10.47) result in
The roots of Eq. (10.49) are given by
The nth normal mode is given by
The free vibration solution of the shaft can be expressed as (see Eq. [10.32])
where the constants and can be determined from the initial conditions of the shaft.
For a uniform circular shaft fixed at and attached to a torsional spring of stiffness at , as shown in Fig. 10.3, the boundary conditions are given by
The free vibration solution of a shaft is given by Eq. (10.27):
The use of the boundary condition of Eq. (10.53) in Eq. (10.55) gives
and the solution can be expressed as
The use of the boundary condition of Eq. (10.54) in Eq. (10.57) yields the frequency equation
Using Eq. (10.26), Eq. (10.58) can be rewritten as
where
The roots of the frequency equation (10.60) give the natural frequencies of vibration of the shaft as
and the corresponding mode shapes as
Finally, the free vibration solution of the shaft can be expressed as
Several possible boundary conditions for the torsional vibration of a uniform shaft are given in Table 10.1, along with the corresponding frequency equations and the mode shapes.
Table 10.1 Boundary conditions of a uniform shaft in torsional vibration.
End conditions of shaft | Boundary conditions | Frequency equation | Mode shape (normal function) | Natural frequencies |
1. Fixed–free |
||||
2. Free–free |
||||
3. Fixed–fixed |
||||
4. Fixed–disk |
||||
5. Fixed–torsional spring |
||||
6. Free–disk |
||||
7. Free–torsional spring |
||||
8. Disk–disk |
The angular displacement of a shaft in torsional vibration can be expressed in terms of normal modes using the expansion theorem, as
where is the ith generalized coordinate. Substituting Eq. (10.64) into Eq. (10.24), we obtain
where and . Multiplication of Eq. (10.65) by and integration from 0 to l yields
In view of the orthogonality relationships, Eqs. (E10.3.8) and (E10.3.10), Eq. (10.66) reduces to
or
Equation (10.67) yields
The solution of Eq. (10.68) is given by
where and denote the initial values of the generalized coordinate and the generalized velocity , respectively.
If the initial conditions of the shaft are given by
Eq. (10.64) gives
By multiplying Eqs. (10.72) and (10.73) by and integrating from 0 to l, we obtain
in view of the orthogonality of normal modes (Eq. [E10.3.8]). Using the initial values of and , Eqs. (10.74) and (10.75), the free vibration response of the shaft can be determined from Eqs. (10.69) and (10.64):
The equation of motion of a uniform shaft subjected to distributed external torque, , is given by Eq. (10.23):
The solution of Eq. (10.77) using modal analysis is expressed as
where is the nth normalized normal mode and is the nth generalized coordinate. The normal modes are determined by solving the eigenvalue problem
by applying the boundary conditions of the shaft. By substituting Eq. (10.78) into (10.77), we obtain
where
Using Eq. (10.79), Eq. (10.80) can be rewritten as
Multiplication of Eq. (10.82) by and integration from 0 to l result in
In view of the orthogonality relationships, Eq. (E10.3.8), Eq. (10.83) reduces to
where the normal modes are assumed to satisfy the normalization condition
and , called the generalized force in nth mode, is given by
The complete solution of Eq. (10.84) can be expressed as
where the constants and can be determined from the initial conditions of the shaft. Thus, the forced vibration response of the shaft (i.e. the solution of Eq. [10.77]), is given by
The steady‐state response of the shaft, without considering the effect of initial conditions, can be obtained from Eq. (10.88), as
Note that if the shaft is unrestrained (free at both ends), the rigid‐body displacement, , is to be added to the solution given by Eq. (10.89). If denotes the torque applied to the shaft, the rigid‐body motion of the shaft, , can be determined from the relation
where denotes the mass moment of inertia of the shaft and indicates the acceleration of rigid‐body motion.
For a shaft or bar of noncircular cross‐section subjected to torsion, the cross‐sections do not simply rotate with respect to one another as in the case of a circular shaft, but they are deformed, too. The originally plane cross‐sections of the shaft do not remain plane but warp out of their own planes after twisting, as shown in Fig. 10.7. Thus, the points in the cross‐section undergo an axial displacement. A function , known as the warping function, is used to denote the axial displacement as
where denotes the rate of twist along the shaft, assumed to be a constant. The other components of displacement in the shaft are given by
The strains are given by
The corresponding stresses can be determined as
The strain energy of the shaft is given by
Defining the torsional rigidity (C) of its noncircular section of the shaft as
the strain energy of the shaft can be expressed as
Neglecting the inertia due to axial motion, the kinetic energy of the shaft can be written as in Eq. (10.11). The work done by the applied torque is given by Eq. (10.12). Hamilton's principle can be written as
The first integral of Eq. (10.99) can be evaluated as
The first integral term on the right‐hand side of Eq. (10.100) can be expressed as (see Eq. [10.97])
The second integral term on the right‐hand side of Eq. (10.100) is set equal to zero independently:
Integrating Eq. (10.102) by parts, we obtain
where is the bounding curve of the cross‐section and is the cosine of the angle between the normal to the bounding curve and the direction. Equation (10.103) yields the differential equation for the warping function as
and the boundary condition on as
Physically, Eq. (10.105) represents that the shear stress normal to the boundary must be zero at every point on the boundary of the cross‐section of the shaft. When Eq. (10.101) is combined with the second and third integrals of Eq. (10.99), it leads to the equation of motion as
and the boundary conditions on as
Love included the inertia due to the axial motion caused by the warping of the cross‐section in deriving the equation of motion of a shaft in torsional vibration [4, 10]. In this case, the kinetic energy of the shaft is given by
where
Note that denotes the axial inertia term. The variation associated with in Hamilton's principle leads to
Denoting
the integrals in Eq. (10.111) can be evaluated to obtain
The first, second, and third terms on the right‐hand side of Eq. (10.114) contribute to the equation of motion, Eq. (10.106), the boundary conditions on , Eq. (10.107), and to the differential equation for , Eq. (10.104), respectively. The new equations are given by
where
In this theory also, the displacement components of a point in the cross‐section are assumed to be [4, 11, 17]
where is not assumed to be a constant. The components of strains can be obtained as
The components of stress are given by
that is,
Note that the effect of Poisson's ratio is neglected in Eqs. (10.130) and (10.131). The strain energy of the shaft can be determined as
where
The variation of the integral can be evaluated as
where
When the second term on the right‐hand side of Eq. (10.138) is integrated by parts, we obtain
The variation of the integral can be evaluated as indicated in Eqs. (10.100), (10.101) and (10.103). The expressions for the kinetic energy and the work done by the applied torque are given by Eqs. (10.108) and (10.12), respectively, and hence their variations can be evaluated as indicated earlier. The application of Hamilton's principle leads to the equation of motion for :
and the boundary conditions
The differential equation for the warping function becomes
with the boundary condition on given by
It is necessary to find the torsional rigidity C of the shaft in order to find the solution of the torsional vibration problem, Eq. (10.106). The torsional rigidity can be determined by solving the Laplace equation, Eq. (10.104):
subject to the boundary condition, Eq. (10.105):
which is equivalent to
Since the solution of Eq. (10.146), for the warping function , subject to the boundary condition of Eq. (10.147) or (10.148) is relatively more difficult, we use an alternative procedure which leads to a differential equation similar to Eq. (10.146), and a boundary condition that is much simpler in form than Eq. (10.147) or (10.148). For this we express the stresses and in terms of a function , known as the Prandtl stress function, as [3, 7]
The stress field corresponding to Saint‐Venant's theory, Eq. (10.95), along with Eq. (10.149), satisfies the equilibrium equations:
By equating the corresponding expressions of and given by Eqs. (10.95) and (10.149), we obtain
Differentiating Eq. (10.151) with respect to z and Eq. (10.152) with respect to y and subtracting the resulting equations one from the other leads to the Poisson equation:
where
is assumed to be a constant. The condition to be satisfied by the stress function on the boundary can be derived by considering a small element of the rod at the boundary as shown in Fig. 10.8. The component of shear stress along the normal direction n can be expressed as
since the boundary is stress‐free. In Eq. (10.155), the direction cosines are given by
where t denotes the tangential direction. Using Eq. (10.149), the boundary condition, Eq. (10.155), can be written as
The rate of change of along the tangential direction at the boundary (t) can be expressed as
using Eqs. (10.156) and (10.157). Equation (10.158) indicates that the stress function is a constant on the boundary of the cross‐section of the rod. Since the magnitude of this constant does not affect the stress, which contains only derivatives of , we choose, for convenience,
to be the boundary condition.
Next we derive a relation between the unknown angle (angle of twist per unit length) and the torque acting on the rod. For this, consider the cross‐section of the twisted rod, as shown in Fig. 10.9. The moment about the x axis of all the forces acting on a small elemental area dA located at the point is given by
The resulting moment can be found by integrating the expression in Eq. (10.160) over the entire area of cross‐section of the bar as
Each term under the integral sign in Eq. (10.161) can be integrated by parts to obtain (see Fig. 10.9):
since at the points and . Similarly,
Thus, the torque on the cross‐section is given by
The function satisfies the linear differential (Poisson) equation given by Eq. (10.153) and depends linearly on , so that Eq. (10.164) produces an equation of the form , where J is called the torsional constant (J is the polar moment of inertia of the cross‐section for a circular section) and C is called the torsional rigidity. Thus, Eq. (10.164) can be used to find the torsional rigidity (C).
Note There are very few cross‐sectional shapes for which Eq. (10.164) can be evaluated in closed form to find an exact solution of the torsion problem. The following example indicates the procedure of finding an exact closed‐form solution for the torsion problem for an elliptic cross‐section.
Prandtl observed that the differential equation for the stress function, Eq. (10.153), is of the same form as the equation that describes the deflection of a membrane or soap film under transverse pressure (see Eq. [13.1] without the right‐hand‐side inertia term). This analogy between the torsion and membrane problems has been used in determining the torsional rigidity of rods with noncircular cross‐sections experimentally [3, 4]. An actual experiment with a soap bubble would consist of an airtight box with a hole cut on one side (Fig. 10.11). The shape of the hole is the same as the cross‐section of the rod in torsion. First, a soap film is created over the hole. Then air under pressure (p) is pumped into the box. This causes the soap film to deflect transversely as shown in Fig. 10.11. If P denotes the uniform tension in the soap film, the small transverse deflection of the soap film (w) is governed by the equation (see Eq. [13.1] without the right‐hand‐side inertia term)
or
in the hole region (cross‐section) and
on the boundary of the hole (cross‐section). Note that the differential equation and the boundary condition, Eqs. (10.166) and (10.167), are of precisely the same form as for the stress function , namely, Eqs. (10.153) and (10.159):
in the interior, and
on the boundary. Thus, the soap bubble represents the surface of the stress function with
or
where denotes a proportionality constant:
The analogous quantities in the two cases are given in Table 10.2.
Table 10.2 Prandtl's membrane analogy.
Soap bubble (membrane) problem | Torsion problem |
G | |
p | |
2 (volume under bubble) |
The membrane analogy provides more than an experimental technique for the solution of torsion problem. It also serves as the basis for obtaining approximate analytical solutions for rods with narrow cross‐sections and open thin‐walled cross‐sections. Table 10.3 gives the values of the maximum shear stress and the angle of twist per unit length for some commonly encountered cross‐sectional shapes of rods.
Table 10.3 Torsional properties of shafts with various cross‐sections.
Cross‐section | Angle of twist per unit length, | Maximum shear stress, | |||||||||||||||||||||
1. Solid circular shaft |
|||||||||||||||||||||||
2. Thick‐walled tube |
|
||||||||||||||||||||||
3. Thin‐walled tube |
|||||||||||||||||||||||
4. Solid elliptic shaft |
|||||||||||||||||||||||
5. Hollow elliptic tube |
|||||||||||||||||||||||
6. Solid square shaft |
|||||||||||||||||||||||
7. Solid rectangular shaft |
|
||||||||||||||||||||||
8. Hollow rectangular shaft |
|||||||||||||||||||||||
9. Solid equilateral triangular shaft |
|||||||||||||||||||||||
10. Thin‐walled tube |
|
The torsional vibration of tapered rods with rectangular cross‐section, pre‐twisted uniform rods, and pre‐twisted tapered rods is presented by Rao [4]. In addition, several refined theories of torsional vibration of rods are also presented in Ref. [4].
The torsional vibration of beams with a rectangular cross‐section is presented by Vet [8]. An overview of the vibration problems associated with turbomachinery is given by Vance [9]. The free vibration coupling of bending and torsion of a uniform spinning beam was studied by Filipich and Rosales [16]. The exact solution was presented and a numerical example was given to point out the influence of whole coupling.
The torsional vibration of beams of thin‐walled open section has been studied by Gere [11]. The behavior of torsion of bars with warping restraint is studied using Hamilton's principle by Lo and Goulard [12].
The coupling between the longitudinal, lateral, and torsional vibrations of a cracked rotor was studied by Darpe et al. [13]. In this work, the stiffness matrix of a Timoshenko beam element was modified to account for the effect of a crack and all six degrees of freedom per node were considered.
The torsional vibration control of a shaft through active constrained layer damping treatments has been studied by Shen et al. [14]. The equation of motion of the arrangement, consisting of piezoelectric and viscoelastic layers, is derived and its stability and controllability are discussed.
The startup torque in an electrical induction motor can create problems when the motor is connected to mechanical loads, such as fans and pumps through shafts. The interrelationship between the electric motor and the mechanical system, which is effectively a multimass oscillatory system, has been examined by Ran et al. [15].
Material of the shaft: steel with and .
Assuming the same wall thickness of the tubes and the same total area of the region occupied by the material (material area), compare the fundamental natural frequencies of the torsional vibration of the shafts. Assume the shaft to be fixed at both the ends.
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