Research Article  Open Access
Free Vibrations of an Elastically Restrained Euler Beam Resting on a Movable Winkler Foundation
Abstract
The traditional theory of beam on elastic foundation implies a hypothesis that the elastic foundation is static with respect to the inertia reference frame, so it may not be applicable when the foundation is movable. A general model is presented for the free vibration of a Euler beam supported on a movable Winkler foundation and with ends elastically restrained by two vertical and two rotational springs. Frequency equations and corresponding mode shapes are analytically derived and numerically solved to study the effects of the movable Winkler foundation as well as elastic restraints on beam’s natural characteristics. Results indicate that if one of the beam ends is not vertically fixed, the effect of the foundation’s movability cannot be neglected and is mainly on the first two modes. As the foundation stiffness increases, the first wave number, sometimes together with the second one, firstly decreases to zero at the critical foundation stiffness and then increases after this point.
1. Introduction
In most previous studies on transverse vibrations of beams, end supports have usually been simplified as rigid restraints such as hinged, fixed, free, or sliding, neglecting the elasticity of end supports. This assumption is certainly convenient for establishing and analyzing the beam theory, while may bring errors or mistakes in some cases. As is known to all, all structural materials possess elasticity to some extent. So, only when the stiffness of end supports is much larger than that of the beam can the assumption of rigid restraints be reasonable. However, in practice, this prerequisite usually cannot be satisfied very well, for example, a submarine pipeline laid on a soft seabed [1] and a girder bridge supported on highly flexible piers [2], for which the elasticity of end supports has to be considered. Till now, a considerable amount of research has been performed on vibration analysis of beams with elastic restraints (e.g., [3–10]), and the influence of stiffness of flexible restraints on beam vibrations has been found significant.
Structural elements that can be represented as a beam supported on an elastic foundation have wide applications in numerous aspects of engineering. Weaver et al. [11] proposed a vibration model for a rigidly restrained beam resting on elastic foundations and derived its general solution. This together with other works sparked off a surge of research in this area that continues in various guises to this day (e.g., [12–18]). And, more recently, the flexibility of end supports of beams on elastic foundation has aroused universal concern of researchers [19–22] and was also found nonnegligible in engineering practice. However, the elastic foundation was usually considered to be fixed with the inertia reference frame in all aforementioned studies of rigidly or elastically restrained beams supported on elastic foundations. To the best of the authors’ knowledge, there is hardly any work done for elastically restrained beams resting on movable elastic foundations, at which some structural elements in the field of engineering can be represented.
We consider in this paper a Euler beam, for simplicity, supported on a movable massless Winkler foundation and with ends elastically restrained by two vertical and two rotational springs, which is one of the most common structures in building and bridge engineering. In Section 2, a general vibration model is developed for the beam. Then, the frequency equations and corresponding mode shapes of the model are analytically derived in Section 3 and can degenerate into many other classical ones. Section 4 presents some numerical examples to study the effects of the movable Winkler foundation as well as elastic restraints on natural characteristics. Finally, some conclusions are summarized in Section 5.
2. Formulation of the Vibration Model
Let us consider a uniform straight Euler beam supported on a movable elastic foundation as shown in Figure 1, where L, A, I, ρ, and E are the span, crosssectional area, crosssectional moment of inertia, beam density, and Young’s modulus of elasticity, respectively. Ends of the Euler beam are elastically restrained by two vertical and two rotational springs with k_{1} and k_{2} being the left and rightend transverse (or vertical) restraint stiffness, respectively, and k_{3} and k_{4} the left and rightend bending restraint stiffness, respectively. The movable Winkler foundation is represented as a rigid massless beam together with distributed springs with a stiffness of k and is plotted above the beam for a clear visibility. As shown in Figure 1, both ends of the rigid beam are hinged to the ones of the Euler beam. So, the Winkler foundation will move vertically and/or rotationally together with the ends of the Euler beam, while has constraint on neither the Euler beam nor the elastic supports. The coordinate system is also shown in Figure 1, where the x axis is defined as the centroidal axis of the Euler beam at its original or static position, and the left end of the beam is located at x = 0. y(x, t) denotes the absolute transverse displacement of the beam relative to the x axis.
The transverse displacements as well as end forces of the Euler beam are detailed in Figure 2 where the movable Winkler foundation is omitted for a clear show. The dotted line A′B′ is the beam’s original or static position, the dashed line AB is the position of the rigid beam due to the elastic supports, and the solid curved AB is the beam’s final position. y(x, t) = the absolute displacement, u(x, t) = the flexural or relative displacement, and (x, t) = the rigidbody or carrier displacement. y(0, t) and y(L, t) are the left and rightend transverse displacement, respectively. All displacement components are supposed to be elastic and linear, hence satisfying the superposition principle. So, y(x, t), u(x, t), and (x, t) can all be considered to act in the same direction, i.e., the vertical direction. Q(0, t) and Q(L, t) denote the shears at two ends, and M(0, t) and M(L, t) denote the end moments. All forces act in their positive direction.
From Figure 2, one obtains
Clearly, (x, t) is determined by y(0, t) and y(L, t) and can be calculated by linear interpolation:
According to Newton’s third law, the end shears and should equal the left and rightend vertical spring loads, respectively,where
Here and evermore, for convenience, , , and so forth.
Considering equations (2), (3a), (3b), (4a), and (4b), equation (1) becomes
Since the inertia force relates to the absolute displacement and the internal force concerns the beam’s deformation, it is easy using Newton’s second law or Hamilton principle to rewrite the classical governing equation of an Euler beam resting on Winkler foundation in dimensionless form aswith boundary conditions given bywhere the prime “” and the over dot “” represent differentiation with respect to the dimensionless coordinate and the dimensionless time , respectively, andwhere and .
Substituting equation (5) into (6) to eliminate yields
Equations (9) and (7a)–(7d) are just the dimensionless freevibration equation and corresponding boundary conditions for the elastically restrained Euler beam resting on a movable Winkler foundation.
3. Frequency Equations and Mode Shapes
3.1. Frequency Equations
Using the method of separation of variables, can be decomposed into spatial function multiplied by temporal function :
Then, substituting equation (10) into (9) gives
This can be separated into two ordinary differential equations given bywhere is the dimensionless frequency and the corresponding dimensional one is .
Accordingly, the boundary conditions in equations (7a)–(7d) become
From equation (12), is sinusoidal in time:where and are the constant coefficients.
The solution of can be assumed aswhere is a constant coefficient, is Euler’s constant, and is the wave number.
When equation (16) is substituted into (13), in order to have a nontrivial solution, the wave number can be solved asfor . The roots are either real or imaginary depending on the frequency (for a given material, geometry and distributed stiffness factor ). When the frequency is greater than , two roots are real and the other two, imaginary. If the frequency is less than , four roots are all imaginary. And, a quadruple zero root is obtained when the frequency is equal to . We call this cutoff frequency the critical frequency . Therefore, we must consider three cases when obtaining spatial solutions, i.e., , , and .
When , the spatial solution is written aswhere for short.
Expressing the exponential function in the above equation in terms of sinusoidal and hyperbolic functions yieldswhere is the real wave number and , , , and are the imaginary unit.
Substituting equation (19) into the boundary conditions in equations (14a)–(14d) yields a system of linear algebraic equations:where , , and the matrix can be expanded into
The determinant of the matrix has to be zero to avoid the trivial solution; then, the frequency equation is obtained aswhere
When , the spatial solution is given bywhere is the real wave number and , , , and .
Similarly, substituting equation (24) into the boundary conditions in equations (14a)–(14d) and making the obtained coefficient matrix singular yields the frequency equationwhere
When , equation (13) becomes
The solution of which is given bywhere () are constants.
Substituting equation (28) into (14a)–(14d) yields a system of linear algebraic equations whose coefficient matrix must be singular to obtain a nontrivial solution. To achieve this requirement, () has to be one root of the following quadratic equation:where
In other words, only when satisfies equation (29) can be one of the natural frequencies of the structure. We call the positive real root of equation (29) the critical foundation stiffness . It should be noted that the number of may be zero, one or two depending on the values of , , , and .
3.2. Mode Shape Functions
Clearly, the aforeobtained frequency equations (22) and (25) are both transcendental ones that have to be solved numerically by the bisection method [23]. After solving for the frequency and the corresponding mode shape, equation (19) or (24) can be determined. For each root of the frequency, there exists one mode shape of vibration which can be obtained as follows.
Without loss of generality, let us consider the case of . Three of the four coefficients () in equation (19) can be solved by three linear algebraic equations in equation (20). Here, we solve , , and from the first three equations. By elementary transformation, we obtainwherewhere
Then, the shape function (19) becomeswhere should be nonzero to represent vibration amplitude.
Clearly, equation (34) is valid when is nonzero. If , the shape function may be obtained by solving coefficients , , and from the first two plus the last linear algebraic equations in equation (20); thus, we can obtain the shape function aswherewhere
4. Calculations and Discussion
4.1. Validation of the Model when
The aforeobtained model can degenerate into other ones by setting and/or () to zero or infinity. means omitting the elastic foundation and infinity corresponds to a rigid beam. Setting (or ) yields a free end. Similarly, a pinned end is achieved by setting infinity and (or infinity and ), a sliding end by setting and infinity (or and infinity), and a fixed end by setting (or ). Table 1 shows the frequency equations and corresponding constants in mode shapes for ten degenerate cases with to validate the present model. They are exactly the same as those given by Blevins and Plunkett [24]. And, Table 2 presents the first five dimensionless wave numbers numerically obtained for the above ten degenerate cases.
