Using a Brace to Design a Soundboard Section for a Desired Natural Frequency
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Transcript of Using a Brace to Design a Soundboard Section for a Desired Natural Frequency
A STRUCTURED APPROACH TO USING A REC-
TANGULAR BRACE TO DESIGN A SOUNDBOARD
SECTION FOR A DESIRED NATURAL FREQUENCY
Patrick Dumond Natalie Baddour
[email protected] [email protected]
Department of Mechanical Engineering
University of Ottawa
161 Louis Pasteur, CBY A205
Ottawa, Canada K1N 6N5
ABSTRACT
The manufacture of acoustically consistent wooden musi-
cal instruments remains economically demanding and can
lead to a great deal of material waste. To address this, the
problem of design-for-frequency of braced plates is con-
sidered in this paper. The theory of inverse eigenvalue
problems seeks to address the problem by creating repre-
sentative system matrices directly from the desired natu-
ral frequencies of the system. The goal of this paper is to
demonstrate how the generalized Cayley-Hamilton theo-
rem can be used to find the system matrices. In particular,
a simple rectangular brace-plate system is analyzed. The
radial stiffness of the plate is varied in order to model
variations typically found in wood which is quartersawn.
The corresponding thickness of the brace required to keep
the fundamental natural frequency of the brace-plate sys-
tem at a desired value is then calculated with the pro-
posed method. It is shown that the method works well for
such a system and demonstrates the potential of using this
technique for more complex systems, including sound-
boards of wooden musical instruments.
1. INTRODUCTION
Many aspects of the manufacture of wooden musical in-
struments have been addressed and rendered consistent.
However, acoustical consistency still remains unattaina-
ble in most situations [1]. This is a consequence of the
fact that the material of choice for many musical instru-
ments is wood, a natural material that exhibits high varia-
bility in its material properties. By definition, wood has
inconsistent properties because its growth is directly re-
lated to the highly variable climate of its environment.
Luthiers have been compensating for these inconsistent
material properties in guitars by means of various meth-
ods for years. The most prominent method currently in
use is to adjust the shape of the soundboard’s braces in
order to attain a more consistent frequency spectrum from
this part of the instrument [2]. These methods have had
varying degrees of success and mostly depend on the skill
and experience of the luthier. Worsening the situation is
the fact that these methods are very labor intensive, ren-
dering them cost-prohibitive, as well as difficult to im-
plement into a structured manufacturing process. For the-
se reasons, most manufacturers only use material that has
mechanical properties which fit within their set criteria.
Such an approach leads to much waste [3].
Like most design problems, a design is first created
from experience and then iteratively refined in order to
achieve the desired parameters. This is especially true of
systems in which certain eigenvalues are desired [4]. For
guitar soundboards, luthiers begin with a certain design,
remove material from the braces in small increments and
then check the system’s natural frequencies (eigenvalues)
until a desired solution converges. It has been shown in
previous work that it is indeed possible to alter certain
frequencies of a soundboard system by simply adjusting
the shape of the braces [5]. While effective, this trial-and-
error method is not optimal. A better approach would be
to design/ construct the system directly from the desired
natural frequencies (eigenvalues).
In order to achieve this, we turn to the field of study
known as inverse eigenvalue problems, which deals spe-
cifically with finding matrices from a set of given eigen-
values [6], [7]. A rather young area, inverse eigenvalue
problems use knowledge of matrix algebra and numerical
methods to create matrices that yield a desired frequency
spectrum (set of eigenvalues) or a partial spectrum. It is
well known that inverse eigenvalue problems are ill-
posed, meaning there generally exists many solutions [7].
In design, the existence of many solutions is potential-
ly beneficial, giving the designer options. However, phys-
ical constraints do need to be applied in order to make a
system physically realizable. Most methods for inverse
eigenvalue problems involve the use of well-developed
matrix theory for matrices with a specific structure (e.g.
Jacobi and band matrices) and then apply appropriate
numerical algorithms to solve for the unknown matrices
from the known desired eigenvalues [8], [9], [10], [11],
[12], [13], [14]. The structure of the matrices generally
implies various physical constraints. However, there exist
very few methods that can solve for matrices having a
more general unstructured form. The goal of this paper is
to demonstrate the use of a technique that has been re-
cently proposed using the generalized Cayley-Hamilton Copyright: © 2013 Patrick Dumond and Natalie Baddour. This is an
open-access article distributed under the terms of the Creative Commons
Attribution License 3.0 Unported, which permits unrestricted use, distri-
bution, and reproduction in any medium, provided the original author
and source are credited.
Proceedings of the Stockholm Music Acoustics Conference 2013, SMAC 2013, Stockholm, Sweden
613
theorem [15]. In particular, this method is interesting
since it allows the use of any matrix structure. Therefore,
a suitable matrix structure can be determined by other
means, for instance from modeling the forward dynamics
of the problem. Implementing particular desired con-
straints thus becomes an exercise of the forward model-
ing process.
In this paper, we apply the Cayley-Hamilton technique
to a simple rectangular brace-plate system in order to
design the combined brace-plate system to a desired natu-
ral frequency. In doing so, we demonstrate that a braced
plate can be designed directly from knowledge of the
desired fundamental frequency. This approach is novel
because it would allow the construction of wooden
soundboards having a consistent set of natural frequen-
cies via design of the braces.
2. MODEL
2.1 Problem Statement
Given a desired fundamental frequency, construct a
brace-plate system as described by a mass matrix M and a
stiffness matrix K.
All mechanical properties of the system are a function
of the radial stiffness ER of the wooden specimen, which
is assumed known and given (and which tends to vary
from specimen to specimen). All dimensional (geometric)
properties of the brace-plate system are assumed to be
specified and fixed except for the thickness of the brace
hc, the design variable for which we must solve.
2.2 Forward Model
The model is based on a typical section of a guitar
soundboard, where a single brace is used to structurally
reinforce the weaker plate direction. The model is shown
in Figure 1.
Figure 1. Orthotropic plate reinforced with a rectangu-
lar brace.
The forward model is discretized using the assumed
shape method, similar to the model used in [5]. The as-
sumed shape method is an energy method which uses
global plate elements within the kinetic and strain energy
plate equations in order to determine the system’s equa-
tions of motion, from which the mass and stiffness matri-
ces are extracted [16]. The system is assumed simply
supported, conservative and the material properties are
assumed orthotropic.
The forward model is created assuming Sitka spruce
and all material properties are related to the radial stiff-
ness of the wood specimen (i.e. the Young’s Modulus in
the radial direction, ER) as indicated in [17]. The use of
ER is chosen because quality control practice observed in
industry use the stiffness across the grain of the wooden
soundboards, measured as in Figure 2.
Figure 2. Quality control measurement of soundboard
plate used in industry
It is assumed that an exact measurement of ER could be
obtained in a similar fashion as that described above and
which could be used in the calculations.
2.3 Inverse Model
The goal of this paper is to reconstruct the brace-plate
system from a desired fundamental frequency. The gen-
eralized Cayley-Hamilton theorem inverse eigenvalue
method is used [15]. The generalized Cayley-Hamilton
theorem states that if p(λ) is the characteristic polynomial
of the generalized eigenvalue problem (K,M), where K
and M are square matrices obtained from p(λ)=det(K-
λM), then substituting (M-1
K) for λ in the polynomial
gives the zero matrix [18], [19]. Thus, by building the
model in the forward sense, and by leaving relevant de-
sign parameters as variable, it is possible to design the
brace-plate model for the fundamental frequency.
It is shown in [20] that in order to adjust the funda-
mental frequency of the brace-plate system to a desired
value, it is necessary to adjust the thickness of the brace.
A cross section of the fundamental modeshape is shown
in Figure 3. It is clear that the brace affects the maximum
amplitude of this modeshape, thus also affecting the as-
sociated frequency [21].
Figure 3. Cross section of the brace-plate system's fun-
damental modeshape
2.4 Cayley-Hamilton Algorithm
Using the facts that the wood’s mechanical properties
vary based on its radial stiffness, and that the brace thick-
ness controls the brace-plate system’s fundamental fre-
quency, the forward model is created using the assumed
Excellent
Good
Mediocre
Discard
Known force
R
0
hp
Ly
x
y z
Lx
0
hc
x1 x2
brace
plate
Proceedings of the Stockholm Music Acoustics Conference 2013, SMAC 2013, Stockholm, Sweden
614
shape method while leaving these two parameters as vari-
ables. Thus, the mass matrix M is a function of hc, the
height of the brace-plate system at the (assumed fixed)
location of the brace, and the stiffness matrix K is a func-
tion of hc and also ER, the plate’s radial stiffness. Here,
we use 2 × 2 trial functions in the assumed shape method.
Hence, 4th
order square matrices are created. The trial
functions used are those of the simply supported rectan-
gular plate such that
1 2
( , , ) sin sin ( )
yx
x y
x y
mmyx
n n
x yn n
n yn xw x y t q t
L L
ππ
= =
= ∑∑ (1)
where m are the modal numbers, q the time function and
w is the displacement variable normal to the plate. The
displacement variable w is then used directly in creating
the kinetic and strain energy equations of the simply sup-
ported rectangular plate. These equations are broken into
three sections as shown in Figure 1 in order to take into
account the brace. This procedure is well described in [5].
It is assumed that the ER of the wood selected for manu-
facture is measured during the manufacturing process and
used as input information into the stiffness matrix. This
leaves hc as the only unknown parameter, appearing in
both the mass and stiffness matrices.
In order to solve these matrices from the desired fun-
damental frequency, the Cayley-Hamilton theorem is
used. To do so, the characteristic polynomial is created
using the desired frequency,
( ) ( ) ( ) ( ) ( )1 2 3p a b b bλ λ λ λ λ= − ⋅ − ⋅ − ⋅ − (2)
where a is the desired frequency and b1-b3 are unknown
values which need to be found. Since we have assumed 2
× 2 trial functions so that the mass and stiffness matrices
are both 4 × 4, the characteristic polynomial must be
fourth order, as shown in equation (2). Subsequently, p(λ)
is expanded so that the polynomials coefficients can be
found. Once the polynomial is created, the Cayley-
Hamilton equation can be written by substituting (M-1
K)
for λ into equation (2).
( )
1 4 1 3
4 3
1 2 1
3 1 0
, ( ) ( )
( ) ( ) 0
p K M c M K c M K
c M K c M K c I
− −
− −
= +
+ + + =
(3)
where cn are the coefficients of λ in p(λ) determined via
equation (2). As stated in [15], equation (3) produces
sixteen equations, of which only four are independent.
Solving the equations on the main diagonal for the four
unknowns (hb, b1, b2, b3) produces 44 = 256 possible solu-
tions, according to Bézout’s theorem [22]. From the set
of all possible solutions, complex solutions can be imme-
diately eliminated as not being physically meaningful.
Clearly, further constraints must be added to the solution
in order to get a solution which fits within the desired
physical limits. These physical limits are based on the
maximum and minimum brace dimensions which are
required to compensate for the range of plate stiffnesses
used during the analysis, as well as the range of natural
frequencies which can be obtained using these system
dimensions. Thus, the following constraints are imple-
mented into the solution:
7 8
1
7 8
2
7 8
3
0.013 0.016 m
1 10 9 10 rad s
1 10 9 10 rad s
1 10 9 10 rad s
bh
b
b
b
≤ ≤
× ≤ ≤ ×
× ≤ ≤ ×
× ≤ ≤ ×
(4)
Solving the four equations obtained from equation (3)
within the constraints provided by (4) yields a physically
realistic solution which satisfies the desired fundamental
frequency, as well as the system’s parameters.
3. RESULTS
3.1 Material Properties
The material used for the brace-plate system during the
analysis is assumed to be Sitka spruce, due to its wide-
spread use in the industry. The mechanical properties of
Sitka spruce are obtained from [17] and are given in Ta-
ble 1.
Material properties Values
Density – µ (kg/m3) 403.2
Young’s modulus – ER (MPa) 850
Young’s modulus – EL (MPa) ER / 0.078
Shear modulus – GLR (MPa) EL × 0.064
Poisson’s ratio – νLR 0.372
Poisson’s ratio – νRL νLR × ER / EL
Table 1. Material properties of Sitka spruce [17].
Since wood is an orthotropic material, the ‘R’ and ‘L’
subscripts used in Table 1 refer to the radial and longitu-
dinal property directions of wood, respectively. The
wood used in making instrument soundboards is general-
ly quartersawn. Therefore the tangential property direc-
tion can be neglected. Since wood properties are highly
variable, the values presented in Table 1 represent a sta-
tistical average and are hence used as a benchmark for
further analysis.
3.2 Model Dimensions
The dimensions used for the model throughout the analy-
sis of the brace-plate system are shown in Table 2.
Dimensions Values
Length – Lx (m) 0.24
Length – Ly (m) 0.18
Length – Lb (m) 0.012
Reference – x1 (m) Lx / 2 – Lb / 2
Reference – x2 (m) x1 + Lb
Thickness – hp (m) 0.003
Thickness – hb (m) 0.012
Thickness – hc (m) hp + hb
Table 2. Dimensions of brace-plate model.
Proceedings of the Stockholm Music Acoustics Conference 2013, SMAC 2013, Stockholm, Sweden
615
These dimensions refer to those shown in Figure 1, where
‘p’ refers to the plate’s dimensions, ‘b’ refers to the
brace’s dimensions and ‘c’ refers to the dimensions of the
combined system. These dimensions are chosen based on
the dimensions of a typical guitar soundboard section
reinforced by a single brace.
3.3 Benchmark Values
In order to demonstrate the working values of the model,
a benchmark is set using the statistical averages for the
properties of Sitka spruce as defined in Table 1. There-
fore, a plate with a radial stiffness of ER = 850 MPa to
which a brace is attached with a combined brace-plate
thickness of hc = 0.015 m is investigated. Using these
values and the forward model, the eigenvalue problem
can be solved to find a fundamental natural frequency of
687 Hz for the brace-plate system. In order to see the
effect on the overall system, the four frequencies pro-
vided using 2 × 2 trial functions are shown in Table 3. In
this case mx and my represent the mode numbers in the x
and y directions respectively.
mx my Natural frequency
(Hz) Modeshapes
1 1 687
2 1 790
2 2 1366
1 2 2648
Table 3. System's natural frequencies at benchmark
values.
3.4 Analysis
After determining the benchmark values, an analysis is
performed using the inverse method described in the pre-
vious section. As the plate’s radial stiffness varies, the
thickness of the brace-plate section is calculated such that
the fundamental frequency of the brace-plate system is
kept consistent at 687 Hz. The results of the computations
can be found in Table 4.
Young’s
modulus
ER (MPa)
Brace
thickness
hc (m)
Fundamental
Frequency
a (Hz)
750 0.01576 687
800 0.01536 687
813 0.01527 687
850 0.01500 687
900 0.01466 687
950 0.01435 687
Table 4. Results of the inverse model analysis.
Clearly, adjusting the thickness of the brace also has an
effect on the other natural frequencies. These can be seen
in Table 5.
Young’s
modulus
ER (MPa)
Brace
thickness
hc (m)
b1
(Hz)
b2
(Hz)
b3
(Hz)
750 0.01576 774 1360 2653
800 0.01536 782 1363 2650
813 0.01527 784 1364 2650
850 0.01500 790 1366 2648
900 0.01466 798 1370 2645
950 0.01435 806 1374 2642
Table 5. Calculated frequencies of the inverse model
analysis.
Interestingly, the constraints indicated in equation (4),
although physically strict, allow for more than one solu-
tion in certain cases. An example is shown in Table 6.
Young’s
modulus
ER (MPa)
Brace
thickness
hc (m)
a
(Hz)
b1
(Hz)
b2
(Hz)
b3
(Hz)
750 0.01359 687 570 1149 2185
Table 6. Alternate brace thickness solution satisfying
the physical constraints.
These results, along with their importance are discussed
below.
4. DISCUSSION
From these results, it is evident that designing a brace-
plate system starting with a desired fundamental frequen-
cy is possible. Table 4 clearly shows that by adjusting the
thickness of the brace by small increments (10-5
m, ma-
chine limit), it is possible to compensate for the variation
in the radial stiffness of the plate (ER) so that the funda-
mental frequency of the combined system is equal to that
of the benchmark value of 687 Hz. The results obtained
using the Cayley-Hamilton theorem algorithm match
those values obtained using the forward model exactly
when compared to the benchmark values in Table 3.
In modifying the thickness of the brace, the fundamen-
tal frequency is not the only frequency which is modified.
Table 5 shows that frequencies b1 to b3 are affected, with
a varying degree of magnitude. To be precise, while fun-
damental frequencies a remain consistent, frequencies b1
to b3 vary by 2%, 0.6% and 0.2% respectively based on
the variation of ER. Therefore, it is important to ensure
that there is a good understanding of what the brace can
control. A detailed discussion of varying the shape of the
brace in order to simultaneously control two natural fre-
quencies is found in [5]. This involves the use of scal-
loped shaped braces such as the one shown in Figure 4.
Using such a brace, one can control both the fundamental
frequency, as well as one of its higher partials simultane-
ously. Furthermore, by increasing the number of variable
parameters such as brace position or number of braces,
many more system frequencies could be controlled.
Proceedings of the Stockholm Music Acoustics Conference 2013, SMAC 2013, Stockholm, Sweden
616
Figure 4. Scalloped shaped brace
Moreover, it was a surprise to find that within the strict
physical constraints of (4), there is more than one brace-
plate system (solution) that satisfies the Cayley-Hamilton
theorem of equation (3). From Table 6 it can be seen that
an alternate solution to the system exists, different from
the one presented in Table 4, for a plate having a radial
stiffness of 750 MPa. In this case, by reducing the thick-
ness of the brace, it is still possible to achieve a system
having the desired frequency of 687Hz. However, the
desired frequency is no longer the fundamental frequency
but rather becomes the second frequency and the funda-
mental has been replaced with a fundamental frequency
of 570 Hz. It is important to keep this phenomenon in
mind while designing a system. This is especially true if
the order in the spectrum of a certain frequency associat-
ed with a certain modeshape is absolutely critical.
In situations requiring the specification of a fundamen-
tal frequency, it is clear that to achieve consistency in this
desired frequency, the thickness of the brace must in-
crease when the stiffness of the plate decreases and vice-
versa. The method demonstrated in this paper provides
for a precise way in which these values can be found.
5. CONCLUSION
In this paper, we demonstrate a direct method for adjust-
ing the natural frequencies of various systems including
musical instruments. The method also directly demon-
strates the ability to compensate for variations in the radi-
al stiffness of wooden plates, thereby making it possible
to create brace-plate systems having a consistent funda-
mental frequency. This structured approach represents a
significant improvement over heuristic methods currently
in use. Although only a simple model was presented in
this paper, the concept of design-for-frequency using the
Cayley-Hamilton method was demonstrated as a proof of
concept for future work in the field of musical acoustics.
It is clear that much work needs to be done in order to
apply this method of design to actual musical instrument
soundboards. However, this technique holds great poten-
tial for creating system matrices of complex systems from
a set of desired frequencies. In doing so, it promises to
greatly benefit the advancement of the manufacturing of
acoustically consistent wooden musical instrument
soundboards.
Acknowledgments
The authors would like to acknowledge the generous
support provided by the Natural Sciences and Engineer-
ing Research Council of Canada.
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