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ME 555-10-07 Final Project Report
1
OPTIMAL SEAT DESIGN FOR AN ENRICHED DRIVING EXPERIENCE
by
Raghavendra Chivukula
Balaji Ramanathan
ME 555-10-07
Winter 2010 Final Project Report
20th
April 2010
ABSTRACT
The design and subsequent optimization of the driver’s seat in a passenger car calls for a
compromise between various aspects – seat comfort, occupant safety, among others. The
complexity of the problem increases when we take into account the variance in the stature of
human occupants, who may be the potential customers of the car. To satisfy the requirements of
a wide range of human population – 5th to 95th percentile of the available population, a lot of
engineering effort is involved in packaging the interior of the car. The design practices suggested
by the Society of Automotive Engineers (SAE) through their J1100 standards and the mandatory
requirements specified by the National Highway Traffic Safety Administration (NHTSA)
through their Federal Motor Vehicle Safety Standards and Regulations (FMVSS), give us a
broad set of guidelines to initiate the design process of the driver’s operational space. However,
the variance in the New Car Assessment (NCAP) ratings obtained by the various cars gives us a
picture of how emphasizing upon one aspect of design might affect the performance with respect
to another aspect. In this study, we have aimed for an optimal design of the driver’s seat in a
passenger car based on the perspectives of seat comfort and occupant safety.
ME 555-10-07 Final Project Report
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Contents
INTRODUCTION ................................................................................................................................... 3
1. SUBSYSTEM DESIGN: SEAT COMFORT (RAGHAVENDRA CHIVUKULA) ........................... 4
1.1. Design Problem Statement ...................................................................................................... 5
1.2. Nomenclature for the seat comfort subsystem ........................................................................ 6
1.3. Model Analysis and Measurement Methods ............................................................................ 7
1.4. Mathematical Model ............................................................................................................. 10
1.5. Monotonicity Analysis............................................................................................................ 18
1.6. Optimization Method and Numerical Analysis........................................................................ 19
1.7. Optimization Study ................................................................................................................ 21
1.8. Parametric Study ................................................................................................................... 25
1.9. Discussion of Results .............................................................................................................. 27
2. SUBSYSTEM OPTIMIZATION: SEAT SAFETY (BALAJI RAMANATHAN) ........................... 29
2.1. Introduction .......................................................................................................................... 29
2.2. Problem Statement and Definitions ....................................................................................... 29
2.3. Range of Motion of the Anchorage Points .............................................................................. 30
2.4. Nomenclature ........................................................................................................................ 31
2.5. Procedure Setup .................................................................................................................... 31
2.6. Design of Experiments ........................................................................................................... 32
2.7. Mathematical Model ............................................................................................................. 33
2.8. Model Analysis ...................................................................................................................... 34
2.9. Numerical Analysis................................................................................................................. 34
2.10. Parametric Study –Constraint Cap Study ................................................................................ 35
3. SYSTEM INTEGRATION ............................................................................................................ 37
3.1. Problem Statement................................................................................................................ 37
3.2. Nomenclature ........................................................................................................................ 38
3.3. Mathematical Model ............................................................................................................. 39
3.4. Numerical Results .................................................................................................................. 43
3.5. Discussion of Results .............................................................................................................. 46
4. REFERENCES .............................................................................................................................. 47
ME 555-10-07 Final Project Report
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INTRODUCTION
The driver cabin design is initiated by fixing the Accelerator Heel Point (AHP) and is continued
thereupon by deciding the seat positioning, determining the reach envelopes, satisfaction of the
visibility criteria, designing the geometrical parameters of the seat and so on. In the early days,
H-point machines were used for the evaluation of various criteria in these studies. However
technological advancements in the recent past, such as the advent of advanced computer models,
have facilitated the virtual performance of the studies over the screen of a computer. Thus in
order to access these analytical tools in our study, we have simplified the driver into a
mechanical model with specified range of motion at the various joints.
The enrichment of driving experience can be obtained when the following primary criteria are
satisfied:
a) Optimal comfort for a human occupant sitting in the seat.
b) Optimal safety to the human occupant in the driver’s seat in the event of a crash/mishap.
Figure 1: Side view of the front cabin of a car
ME 555-10-07 Final Project Report
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Thus the problem of designing for an optimal driving experience can be divided into two
subsystems in the lines of the aforementioned criteria. The delineation of the subsystems is as
follows:
1. Geometric features and construction of the seat for optimum comfort to the human
occupant.
2. Optimal seat belt anchorage positions of a three point belt for providing ample safety to the
driver.
The overall objective of this study being driver’s comfort is the overall objective through the
calculation and the subsequent minimization of a driver discomfort index, which imparts weight
age to each of the subsystems towards the optimization of the overall driving experience.
Literature required for the project has been sourced from the exhaustive research done in the
field of driver safety and biomechanics at the University of Michigan Transportation Research
Institute [UMTRI].
1. SUBSYSTEM DESIGN: SEAT COMFORT (RAGHAVENDRA CHIVUKULA)
Design for comfort in the seat of a passenger car is critical in view of the economic costs (both to
the driver and the manufacturer) associated with medical conditions such as lumbar disk
herniation and cutaneous ischemia resulting from improper design.
Figure 2: A bucket seat in a car with design similar to this study
The comfort in an automobile seat is one of the most easily realized features of the driving
experience. However, in a manner of stark contrast, the objective analysis and interpretation of
ME 555-10-07 Final Project Report
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comfort is a matter of immense complexity as comfort is widely viewed as a subjective
perception varying from one individual to another. In this study we use the functional definition
of comfort as the lack of discomfort inducing stimuli. Thus we strive towards the minimization
of these stimuli for obtaining maximum comfort, even as we check the economic and ergonomic
costs associated with seat design- in terms of the volume of the seat.
1.1. Design Problem Statement
The objective of this subsystem is to design a seat of minimum volume without compromising
on the comfort of the driver. In this study the seat is subdivided into the seat cushion and the
backrest, in order to facilitate better delineation of the geometric parameters of the seat. This
would also enable an improved understanding of the role of each design variable in the
discomfort experienced by the driver and also the correlation and tradeoffs involved in the design
of different geometric features. The design of the headrest is not included in this design.
Both the cushion and the back rest are primarily designed in view of the anthropometric
measurements of the human populations.
In the design of seat the pressure acting at the Ischial Tuberosities is considered as the major
source of discomfort. Excessive pressure can lead to a host of complications such as pain in the
hip to occlusion of blood vessels - due to deformation of the skin and underlying tissues- leading
to cutaneous ischemia.
In the design of backrest apart from the necessity of ample field of vision, the support offered by
the seat to the Lumbar Spine is considered as an important feature of design. The backrest is
designed to maintain Lumbar Lordotic posture in conjunction with Thoracic Kyphotic posture,
for in this posture the stress on the spinal cord would be minimal.
ME 555-10-07 Final Project Report
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1.2. Nomenclature for the seat comfort subsystem
Table 1: Nomenclature for the seat comfort subsystem
Index Symbol Description Unit
1 αc Seat cushion angle degrees
2 αb Backrest angle degrees
3 Cs Scale factor for seating area calculation 1
4 Cit Scale factor for pressure at Ischial Tuberosities 1
5 Cl Scale factor for pressure at Lumbar spine 1
6 g Acceleration due to gravity m/s2
7 H H-point 1
8 Hl Lumbar height mm
9 Lb Length of the backrest mm
10 Lc Length of the cushion mm
11 M Mass of the human occupant kg
12 Pit Pressure at the Ischial Tuberosities N/ mm2
13 Pl Pressure at the Lumbar spine N/mm2
14 Pm Pelvis mass value 1
15 Rl Radius of curvature of the Lumbar support mm
16 Rt Radius of curvature of the Thoracic support mm
17 Sc Surface area of the cushion mm2
18 Sl Surface area of the Lumbar support section mm2
19 Ss Seating Surface area mm2
20 T Thickness of the cushion and backrest mm
21 Tm Torso mass value 1
22 θl Lumbar Lordosis angle degrees
23 θt Thoracic Kyphosis angle degrees
24 Vbc Volume of the backrest at chest or upper back mm3
25 Vbw Volume of the backrest at waist or lower back mm3
ME 555-10-07 Final Project Report
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26 Vc Volume of the cushion mm3
27 Vs Volume of the seat mm3
28 Wbc Width of the backrest at chest or upper back mm
29 Wbw Width of the backrest at waist or lower back mm
30 Wc Width of the cushion mm
1.3. Model Analysis and Measurement Methods
The seat design parameters are broadly classified into four categories based on their contribution
to the seating comfort of the human occupant:
1. Fit Parameters: The level of these parameters is determined by the anthropometry of the
occupant population and depends on the level of fit achieved by an occupant of certain
anthropometric measurements. The fit parameters employed in the seat design and their
corresponding measurement methods are as follows:
a) Length of the cushion (Lc) is the dimension measured along the thigh line from the
front of the seat cushion to the depressed surface of the seatback.
b) Width of the cushion (Wc) is the maximum dimension measured laterally across the
cushion and it is considered to be uniform from the front of the cushion to the hips.
c) Thickness of the cushion (Tc) is the distance from the seating surface of the cushion to
the underside of the cushion and is measured perpendicular to the non-deformed seating
surface.
d) Length of the backrest (Lb) is the dimension measured along the torso/manikin line
from the depressed surface of the seat cushion to the top of the seat back soft trim.
e) Width of the backrest at the waist or lower back (Wbw) is the maximum dimension
measured laterally across the backrest at the waist level and perpendicular to the
torso/manikin line.
f) Width of the backrest at the chest or upper back (Wbc) is the maximum dimension
measured laterally across the backrest at the chest level and perpendicular to the
torso/manikin line.
g) Thickness of the backrest (Tb) is the distance from the backrest surface to the underside
of the backrest and is measured perpendicular to the non-deformed backrest surface.
ME 555-10-07 Final Project Report
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Figure 3: Illustration of Fit Parameters
2. Support parameters: These parameters affect the posture of the human occupant. They
are determined by the anatomy of the human body and the stress induced in different
segments of human when subjected to various postures. The support parameters employed
in the seat design are as follows:
a) Radius of curvature of the Lumbar support (Rl) is the longitudinal radius of curvature in
the lower back region along with a prominence.
b) Radius of curvature of the Thoracic support (Rt) is the longitudinal radius of curvature
in the chest region along with a depression.
c) Lumbar Lordosis angle (θl) is the curvature of the lordotic curve in the lumbar region of
the spine.
d) Thoracic Kyphosis angle (θt) is the curvature of the thoracic vertebrae which composes
the middle segment of the vertebral column.
Lb
Lc
T
Ws
Wbw
Wbc
ME 555-10-07 Final Project Report
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Figure 4: Illustration of Support Parameters and Seat Adjustment angles
3. Seat adjustment angles: These angles are adjustment features provided to the seat cushion
and backrest to facilitate the comfort of the human occupant in seating and during ingress
and egress. The seat adjustment angles are as follows:
a) Seat cushion angle (αc) is the angle measured between the thigh centerline and the
horizontal.
b) Backrest angle (αb) is the angle measured between torso/manikin centerline and the
horizontal.
4. Feel Parameters: These parameters are related to the physical contact between the
occupant and the seat and are directly related to the sensory perceptions of the human
occupant. The feel parameters employed in the seat design are as follows:
a) Pressure at the Ischial Tuberosities (Pit), which is the peak pressure in the seat cushion
experienced at the ischii due to flexion of the hip joint in the seating posture.
Height of the backrest
Seat Cushion angle
Backrest angle
Radius of Curvature of Lumbar Support
Radius of Curvature of Thoracic Support
Min. Lumbar Height
ME 555-10-07 Final Project Report
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b) Pressure in the region of Lumbar spine (Pl) from L2-L5 assists in maintaining Lumbar
Lordosis, thereby reducing the incidence and intensity of back ache.
Scale factors employed:
The following scale factors have been employed to facilitate the ease of calculation:
a) The scale factor of seating area calculation (Cs) ) [ Expresses the seating surface area with
respect to the surface area of the cushion(Sc)]
b) The scale factor for pressure at Ischial Tuberosities (5)
(Cit) ) [ Expresses the pressure on the
Ischial Tuberosities region(Pit) with respect to the mean pressure over the cushion]
c) The scale factor for pressure at Lumbar Spine (7)
(Cl) [Expresses the pressure on the
Lumbar spine region (Pl) with respect to the mean pressure over the backrest].
d) The Pelvis mass value(6)
(Pm) [ Expresses the mass of the pelvis relative to the body mass]
e) The Torso mass value(6)
(Tm) ) [Expresses the mass of the torso relative to the body mass]
1.4. Mathematical Model
Objective Function:
The objective of the seat comfort subsystem optimization design is to minimize the volume of
the seat, while maintaining satisfactory comfort levels to the human occupant in terms of fit,
support and feel parameters.
The choice of minimization of the volume of the seat is a consequence of the primary objective
of minimizing the weight of the seat. However upon assuming the seat to be uniform in
construction (for the simplicity of the design model), passing the density of the seat as a
parameter would not be of any particular interest in the design of seat for comfort. Hence the
additional redundant parameter of density is avoided and the objective function is structured to
minimize the volume.
The Objective function is modeled as follows:
Minimize
Volume of seat (Vs) = Volume of the cushion (Vc) + Volume of the backrest (Vb)
𝑓 = 𝑉𝑠 = 𝐿𝑐𝑊𝑐𝑇𝑐 + 𝑊𝑏𝑤. 𝜋. 𝜃𝑙
360 𝑅𝑙 +
𝑇
2
2
− 𝑅𝑙 −𝑇
2
2
+ 𝑊𝑏𝑐. 𝜋. 𝜃𝑡
360 𝑅𝑡 +
𝑇
2
2
− 𝑅𝑡 −𝑇
2
2
ME 555-10-07 Final Project Report
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Constraints:
The constraint functions are obtained on the basis of functional definition of comfort as it is
applied to seating. Comfort in seating can be expressed as a state of reduced discomfort. Thus the
aim of the seat design would be to reduce or eliminate the factors causing discomfort such as a
cushion that is too long or a backrest that lacks lumbar support, among others.
Thus for this project the following constraints have been employed to decrease the discomfort
inducing factors. The choice of the constraints is based on the level of detail and scope of the
project, with many other constraints being excluded because of the difficulty in their
mathematical formulation and/or the complexity added to the optimization problem.
The constraints are structured along the four parameters of seat design as explained in the
previous section. The constraint set is sourced from the literature listed in the References and is a
product of exhaustive study on human test subjects and human anatomy.
Note: The constraints were originally structured in reference to the H-Point which is the pivot
center of the torso and thigh on the two-or three- dimensional devices used in defining and
measuring vehicle seat accommodation(1)
. For the convenience of interpretation the
measurements along the H-Point manikin backrest line where scaled up by assuming a 95-mm
distance from the point of maximum deflection of the seat surface to the H-point (1)
. Similarly the
measurements on the H-Point thigh line where scaled up by assuming a 135 mm distance from
H-Point to the depressed backrest surface.
Fit Constraints
a) The length of the seat cushion (Lc) is a critical parameter for comfort since a cushion which
is too long can put pressure on the back of the sitter's legs near the knee, an area that has
many superficial nerves and blood vessels. Pressure in this area will lead to local
discomfort and restricted blood flow to the legs. Second, a cushion that is too long will pull
sitters forward, away from the backrest, eliminating the possibility of providing appropriate
lumbar support(2)
. While a shorter cushion would deprieve the occupant from ample
support beneath the thighs.
According to Grandjean (1980) recommendations the seat cushion length (Lc) is bounded
below at 440 mm and above at 550 mm.
ME 555-10-07 Final Project Report
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𝑔1 = 440 − 𝐿𝑐 ≤ 0
𝑔2 = 𝐿𝑐 − 550 ≤ 0
b) The hip dimensions of 95th
percentile female population is considered for determining the
width of the seat cushion. Thus the seat cushion should be 500 mm wide at the hips. The
front of the cushion should also have a minimum of 500 mm width to allow for
comfortable leg splay. Thus we employ a lower bound of 500 mm for the seat cushion
width(Wc)
𝑔3 = 500 − 𝑊𝑐 ≤ 0
c) Minimum backrest width at the waist level is constrained by the back width of the large
male segment of the population (2)
.
The backrest should be a minimum of 360 mm wide at the waist or lower back region
(Wbw) and a minimum of 456 mm wide at the chest or upper back region(2)
(Wbc). The
division of the backrest between these widths is affected by Rl , Rt, θl and θt.
𝑔4 = 360 − 𝑊𝑏𝑤 ≤ 0
𝑔5 = 456 − 𝑊𝑏𝑐 ≤ 0
d) The bounds for the thickness of the seat (T) have been determined from empirical data. The
thickness of the seat is bounded below at 100 mm and above at 120 mm.
𝑔6 = 100 − 𝑇 ≤ 0
𝑔7 = 𝑇 − 120 ≤ 0
e) Backrest length (Lb) requirements are affected by geometric constraints imposed by
FMVSS 202 (U.S. Office of the Federal Register 1992) dealing with head restraints for
protection in rear impacts (2)
.
We employ Gordon et al. recommendations (3)
for the backrest height (Lb), according to
which Lb is bounded below at 509 mm and above at 646 mm.
𝐿𝑏 = 2𝑅𝑙. 𝑠𝑖𝑛𝜋. 𝜃𝑙
360+ 2𝑅𝑡. 𝑠𝑖𝑛
𝜋. 𝜃𝑡
360
𝑔8 = 509 − 2𝑅𝑙. 𝑠𝑖𝑛𝜋. 𝜃𝑙
360− 2𝑅𝑡. 𝑠𝑖𝑛
𝜋. 𝜃𝑡
360≤ 0
𝑔9 = 2𝑅𝑙. 𝑠𝑖𝑛𝜋. 𝜃𝑙
360+ 2𝑅𝑡. 𝑠𝑖𝑛
𝜋. 𝜃𝑡
360− 646 ≤ 0
ME 555-10-07 Final Project Report
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Support Constraints
a) The Lumbar support should be sufficiently padded to avoid discomfort due to high
pressure. Ideally the support should be adjustable. However for this project the support is
assumed to be fixed and the support is defined on the basis of its longitudinal curvature.
According to the recommendations of Floyd and Roberts (2)
(1958) the Lumbar support
curvature (Rl) is bounded below at 400 mm and above at 460 mm.
𝑔10 = 400 − 𝑅𝑙 ≤ 0
𝑔11 = 𝑅𝑙 − 460 ≤ 0
b) The Thoracic support curvature (Rt) is not extensively researched in the seat design and is
generally assumed to be flat. However for the purpose of this project we bound (3)
Rt below
at the upper bound of Rl and above at 500 mm.
𝑔12 = 460 − 𝑅𝑡 ≤ 0
𝑔13 = 𝑅𝑡 − 500 ≤ 0
c) On the basis of anatomical studies (4)
, the Lumbar Lordosis angle (θl) angle is bounded
below at 40 deg and above at 60 deg.
𝑔14 = 40 − 𝜃1 ≤ 0
𝑔15 = 𝜃1 − 60 ≤ 0
d) On the basis of anatomical studies (4)
, the Thoracic Kyphosis angle (θt) angle is bounded
below at 20 deg and above at 40 deg.
𝑔16 = 20 − 𝜃𝑡 ≤ 0
𝑔17 = 𝜃𝑡 − 40 ≤ 0
e) The height of the apex of the Lumbar support (Hl) is very critical for the comfort of the
human occupant. Ample support can be offered to the Lumbar spine if the apex of the
Lumbar support curvature falls in the region of L5-L2 vertebrae of the Lumbar spine. Thus
we employ modified Reed et al.(2)
recommendations for the Lumbar Height(Hl) which
constraint the Hl below at 200 mm and above at 250 mm.
𝐻𝑙 = 𝑅𝑙. 𝑠𝑖𝑛 𝜋𝜃𝑙
360
ME 555-10-07 Final Project Report
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(The factor π/180 is employed for conversion of the angle from degrees to radians to be
compatible for use in MATLAB.)
𝑔18 = 200 − 𝑅𝑙. 𝑠𝑖𝑛𝜋. 𝜃𝑙
360≤ 0
𝑔19 = 𝑅𝑙. 𝑠𝑖𝑛𝜋. 𝜃𝑙
360− 250 ≤ 0
Feel Constraints
The feel constraints employed in the seat design are the peak pressures acting in the critical
regions of the seat cushion and backrest.
As described in the previous section the critical region in the seat cushion is the region near the
Ischial Tuberosities. In order to provide ample comfort, the pressure at the Ischial Tuberosities
(Pit) is bounded above at 3 kN/m2.
Pit=𝑔20 = 𝐶𝑖𝑡. 𝑀. 𝑔. 𝑃𝑚. 𝑐𝑜𝑠 𝜋.𝛼𝑐
180 / 𝐶𝑠. 𝐿𝑐. 𝑊𝑐 – (3𝑒 − 3) ≤ 0
where
The seating surface area (Ss) = Cs.Lc.Wc
The scale factor of seating area calculation (Cs) = (432/500)
The scale factor for pressure at Ischial Tuberosities(5)
(Cit) = 3.624
The Pelvis mass value (6)
(Pm) =
The acceleration due to gravity (g) = 9.8 m/s2
Pressure in the region of Lumbar spine plays a critical role in maintaining the prescribed posture
of Lumbar Lordosis, which subjects the Lumbar vertebrae to lesser stress levels when compared
to other postures. Thus adequate Lumbar support of the backrest is necessary for maintaining this
posture and the pressure at the Lumbar spine is consequently bounded below at 2.5 kPa for the
comfort of the human occupant.
Pl = 𝑔21 = 2.5𝑒 − 3 − 𝐶𝑙. 𝑀. 𝑔. 𝑇𝑚. 𝑐𝑜𝑠(𝜋.180−𝛼𝑏
180)/ 2𝜋. 𝜃𝑙. 𝑊𝑏𝑤. (𝑅𝑙 +
𝑇
2)/360 ≤ 0
0.2997 (for men); 0.3157 (for women)
ME 555-10-07 Final Project Report
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where
The surface area of the lumbar section (Sl) = 2𝜋. θl. Wbw. (Rl +T
2)/360
The scale factor for pressure at Lumbar Spine (7)
(Cl) = 0.719
The Torso mass value (6)
(Tm) = 0.3213 (for men); 0.3092 (for women)
The acceleration due to gravity (g) = 9.8 m/s2
Design Variables, Parameters and Constants:
Table 2: Design variables, parameters and constants
Symbol Description Type
Lc Length of the cushion Variable
Wc Width of the cushion Variable
Wbw Width of the backrest at waist or lower back Variable
Wbc Width of the backrest at chest or upper back Variable
T Thickness of the cushion and backrest Variable
Rl Radius of curvature of the Lumbar support Variable
Rt Radius of curvature of the Thoracic support Variable
θl Lumbar Lordosis angle Variable
θt Thoracic Kyphosis angle Variable
αc Seat cushion angle Parameter
αb Backrest angle Parameter
Pm Pelvis mass value Parameter
Tm Torso mass value Parameter
M Mass of the human occupant Parameter
Cs Scale factor for seating area calculation Parameter
Cit Scale factor for pressure at Ischial Tuberosities Parameter
Cl Scale factor for pressure at Lumbar spine Parameter
g Acceleration due to gravity Constant
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The values of the parameters and constants employed in this study are as follows:
Parameters:
Seat Cushion angle (αc) = (10,15,20,25) deg.
Backrest angle (αb) = (105,110,115,120) deg.
The Pelvis mass value(6)
(Pm) = 0.2997 (for men)
0.3157 (for women)
The Torso mass value(6)
(Tm) = 0.3213 (for men)
0.3092 (for women)
Constants:
Mass of the Human Occupant (M) = 70 kg
The scale factor of seating area calculation (Cs) = (432/500)
The scale factor for pressure at Ischial Tuberosities(5)
(Cit) = 3.624
The scale factor for pressure at Lumbar Spine(7)
(Cl) = 0.719
The acceleration due to gravity (g) = 9.8 m/s2
Summary Model:
Objective function
Minimize
𝑉𝑠 = 𝐿𝑐𝑊𝑐𝑇𝑐 + 𝑊𝑏𝑤 .𝜋 .𝜃𝑙
360 𝑅𝑙 +
𝑇
2
2
− 𝑅𝑙 −𝑇
2
2
+ 𝑊𝑏𝑐 .𝜋 .𝜃𝑡
360 𝑅𝑡 +
𝑇
2
2
− 𝑅𝑡 −𝑇
2
2
subject to:
𝑔1 = 440 − 𝐿𝑐 ≤ 0
𝑔2 = 𝐿𝑐 − 550 ≤ 0
𝑔3 = 500 − 𝑊𝑐 ≤ 0
𝑔4 = 360 − 𝑊𝑏𝑤 ≤ 0
𝑔5 = 456 − 𝑊𝑏𝑐 ≤ 0
𝑔6 = 100 − 𝑇 ≤ 0
𝑔7 = 𝑇 − 120 ≤ 0
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𝑔8 = 509 − 2𝑅𝑙. 𝑠𝑖𝑛𝜋. 𝜃𝑙
360− 2𝑅𝑡. 𝑠𝑖𝑛
𝜋. 𝜃𝑡
360≤ 0
𝑔9 = 2𝑅𝑙. 𝑠𝑖𝑛𝜋. 𝜃𝑙
360+ 2𝑅𝑡. 𝑠𝑖𝑛
𝜋. 𝜃𝑡
360− 646 ≤ 0
𝑔10 = 400 − 𝑅𝑙 ≤ 0
𝑔11 = 𝑅𝑙 − 460 ≤ 0
𝑔12 = 460 − 𝑅𝑡 ≤ 0
𝑔13 = 𝑅𝑡 − 500 ≤ 0
𝑔14 = 40 − 𝜃𝑙 ≤ 0
𝑔15 = 𝜃𝑙 − 60 ≤ 0
𝑔16 = 20 − 𝜃𝑡 ≤ 0
𝑔17 = 𝜃𝑡 − 40 ≤ 0
𝑔18 = 200 − 𝑅𝑙. 𝑠𝑖𝑛𝜋. 𝜃𝑙
360≤ 0
𝑔19 = 𝑅𝑙. 𝑠𝑖𝑛𝜋. 𝜃𝑙
360− 250 ≤ 0
𝑔20 = 𝐶𝑖𝑡. 𝑀. 𝑔. 𝑃𝑚. 𝑐𝑜𝑠 𝜋.𝛼𝑐
180 / 𝐶𝑠. 𝐿𝑐. 𝑊𝑐 – (3𝑒 − 3) ≤ 0
𝑔21 = 2.5𝑒 − 3 − 𝐶𝑙. 𝑀. 𝑔. 𝑇𝑚. 𝑐𝑜𝑠(𝜋.180 − 𝛼𝑏
180)/ 2𝜋. 𝜃𝑙. 𝑊𝑏𝑤. (𝑅𝑙 +
𝑇
2)/360 ≤ 0
Set Constraints:
Lc, Wc, Wbw,Wbc, T, Rl, Rt ≥ 0
θl, θt ≥ 0 deg; θl, θt≤ 90 deg
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1.5. Monotonicity Analysis
Table 3:Monotonicity Analysis
Lc Wc Wbw Wbc T Rl Rt θl θt
f + + + + + + + + +
g1 -
g2 +
g3 -
g4 -
g5 -
g6 -
g7 +
g8 - - - -
g9 + + + +
g10 -
g11 +
g12 -
g13 +
g14 -
g15 +
g16 -
g17 +
g18 - -
g19 + +
g20 - -
g21 + + + +
Discussion of Monotonicity Analysis and activity of constraints:
From the Monotonicity Analysis in Table-3, we can realize the following features with regard to
the behavior of the objective function and the constraints:
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1. The objective function deals with the volume of the seat and hence is heavily monotonic
with respect to the design variables. The volume of the seat depends on the geometric
parameters involved in the construction of the seat and upon observing the objective
function it would be evident to us that increase in any of the design variables- which are the
geometric parameters in seat design- would consequently increase the volume of the seat.
This observation explains the monotonically increasing behavior of the objective function
with respect to all the design variables.
2. Both the constraints g1 and g20 have opposite monotonicity to that of f with respect to Lc.
Hence activity of either of the constraints cannot be deduced from monotonicity analysis.
Since neither of them is uniquely critical, they form a conditional critical set in which either
of them can be active.
3. Similarly
a) g3 and g20 form a conditionally critical set in which either of them can be active with
respect to Wc.
b) g8, g10 and g18 form a conditionally critical set in which either of them can be active
with respect to Rl.
c) g8 and g12 form a conditionally critical set in which either of them can be active with
respect to Rt.
d) g8, g14 and g18 form a conditionally critical set in which either of them can be active
with respect to θl.
e) g8 and g16 form a conditionally critical set in which either of them can be active with
respect to θt.
4. By Monotonicity Principle 1 we can realize that:
a) g4 is active and critical with respect to Wbw.
b) g5 is active and critical with respect to Wbc.
c) g6 is active and critical with respect to T.
1.6. Optimization Method and Numerical Analysis
The optimization study is carried out by employing fmincon solver from the optimization
toolbox of MATLAB. The optimum solution is evaluated through an iterative procedure based
on Sequential Quadratic Programming.
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In this routine Active set algorithm was employed which searches for the solution by checking
for the validity of Karush-Kuhn Tucker ( KKT ) conditions. The KKT conditions are the
necessary conditions for the optimality of the constrained optimization problem. In this process
the activity of the constraints is also evaluated through the computation of values of Langrange
multipliers of the KKT equations; with any multiplier having a value equal to zero being
associated with an inactive constraint.
Line search is employed in the iterations and the use of Quasi Newton Hessian approximation
ensures super linear convergence.
The exploration of the solution through the sole use of fmincon solver has been influenced by the
following factors:
a) The optimization problem being a non-linear constrained problem.
b) The robustness of the optimization algorithm of fmincon.
c) The heavy monotonicity of the objective function with respect to the design variables and
the presence of both upper and lower bounds on a majority of variables gives a preliminary
suggestion of convergence to a global optimum, thus imposing faith in the solution of a
single optimization tool (However this intuition needs to be verified as done in the
subsequent section).
The results from the fmincon solver are as follows:
Table 4: Results from fmincon solver
Lc Wc Wbw Wbc T Rl Rt θl θt
Starting
Point 540 1000 1000 1000 90 410 450 59 25
Value at
the
solution
521.21 500.20 360 456 100 460 460 51.40 20
The volume of the seat at this set of design variables = 4.8251 * 107 mm
3.
This solution was computed by setting the parameters at:
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Pm = 0.2997; Tm = 0.3213; αc = 25 deg; αb=105 deg.
The level of the design variables is shown in Figure 4.
Figure 5: Level of Design Variables
1.7. Optimization Study
Upon reviewing the results of the optimization process we can observe that the iterative search
ends at a possible value of local minimum that satisfies the constraints as indicated by the output
of ‘exitflag = 4’. The solution is referred to as possible local minimum as the search stopped due
to size of the search direction being less than twice the default value of step size tolerance. The
attainment of local minimum can be verified by checking the value of the first order optimality
measure, the value of the violation of the constraints at the obtained solution and by employing
different starting points; as done in the following analysis.
The significant results of the optimization process are discussed below:
a) The first order optimality measure (= 3.3204*10-6
) is close to the default value (= 1*10-6
).
This indicates that the solution is sufficiently close to the optimal. This behavior is shown in
Figure 5.
1 2 3 4 5 6 7 8 90
100
200
300
400
500
600
Number of variables: 9
Cur
rent
poi
nt
Current Point
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b) The violation of constraints at the optimal solution (= 3.8207*10-16
) is also less than the
default value (= 1*10-6
) indicating the validity of the solution. This behavior is shown in
Figure 6.
Figure 6: Function value
Figure 7: First order optimality measure
0 2 4 6 8 10 12 144
5
6
7
8
9
10
11
12x 10
7
Iteration
Fun
ctio
n va
lue
Current Function Value
0 2 4 6 8 10 12 140
2
4
6
8
10
12
14x 10
6
Iteration
Firs
t-or
der op
timal
ity
First-order Optimality
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c) The activity of constraints from the ‘Active inequalities’ output of MATLAB can be
analyzed as follows:
1. The variables that touch the lower bound are Wbw, Wbc, T, Rt and θt. This verifies the
activity and criticality of constraints g4 with respect to Wbw; g5 with respect to Wbc and
g6 with respect to T. It also identifies the activity of constraints g12 with respect to Rt
and g16 with respect to θt.
2. The variable that touches the upper bound is Rl; this verifies the inactivity of the
constraint g10 with respect to Rl. Upon further analysis by plugging in the values of Rl
and θl obtained from the optimization process, we realize that the constraint g8 is active
with respect to both Rl and θl, while g18 constraint is inactive for these variables.
Note: In this regard it is observed that although the volume decreases with decrease in
both Rl and θl , the search for the minimum volume is carried by decreasing the value
of θl while correspondingly increasing Rl to maintain the equality of g8 (with inequality
constraint now being active). Thus the value of is Rl increased until it is bounded above
by g11, making the upper bound active
3. MATLAB further confirms the activity of the non-linear inequality constraint g8. The
non linear inequality constraint g20 is also classified to be an active constraint. By
plugging the values of Lc and Wc we can realize that g20 is active with respect to these
variables.
It can be realized the values of the Lagrangian multipliers are greater than or equal to zero (with
the equality arising for the case of inactive constraints and inequality for the active constraints-
g4, g5, g6, g8, g11, g12, g16 and g20). This is consistent with the KKT conditions, which are to
be satisfied to attain a feasible solution for a constrained optimization problem. Thus the flag that
local minimum is obtained indicates the satisfaction of KKT conditions.
Now the robustness of the solution can be checked by starting from different values of the design
variables. For this study we employ 3 starting points each for the variables Lc ,Wc and θl. The
other design variables meet their bounds and hence changing the starting point of any such
variable would not affect the solution, when the starting points of other variables are held
constant.
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The strategy adopted for this study involves each variable being swept across its feasible space,
by sampling four points from the feasible space while the starting points of other variables are
held constant. The sampling points chosen are – the lower bound, upper bound and two
intermediate values in the feasible space of these variables. This apart the solution is also verified
for the two cases of Lc ,Wc and θl , simultaneously starting at their lower bounds and upper
bounds. The results of this study are recorded in the Table-5 shown below:
Table 5: Study of robustness by choosing different starting points for Lc, Wc and θ1
Starting Points Lc(mm) Wc(mm) θl(mm) Vs
(Volume) (mm3)
(440,500,40) 483.4615 539.2669 51.4504 4.8251 * 107
(440,1000,59) 519.4653 501.8907 51.4054 4.8251 * 107
(480,1000,59) 521.2252 500.1941 51.4054 4.8251 * 107
(520,1000,59) 521.2179 500.2030 51.4054 4.8251 * 107
(550,1000,59) 521.2112 500.2095 51.4054 4.8251 * 107
(540,500,59)*
440.0192 592.5078 51.4054 4.8251 * 107
(540,700,59)*
521.3998 500.0286 51.4054 4.8251 * 107
(540,1000,59)*
521.2110 500.2097 51.4054 4.8251 * 107
(540,1800,59)*
519.0817 502.2616 51.4054 4.8251 * 107
(540,1000,40) 440.0147 592.5138 51.4054 4.8251 * 107
(540,1000,47) 440.5046 591.8549 51.4054 4.8251 * 107
(540,1000,53) 442.2441 589.5269 51.4054 4.8251 * 107
(540,1000,60) 521.4296 500 51.4054 4.8251 * 107
(550,1800,60)*
474.7604 549.1503 51.4054 4.8251 * 107
* The upper bound for Wc being infinity, intermediate values above 500 are chosen for analysis.
By this study we can be observe that:
a) The value of the objective function [4.8251*107mm
3] remains the same irrespective of the
starting point. Hence it can be assumed we obtain a local minimum which is independent of
the choice of the starting points.
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b) The value of Lumbar Lordosis angle (θl) remains the same irrespective of the starting point
because of the active upper bound on the radius of curvature of the Lumbar Support (Rl).
c) The design variables always lie within their respective feasible space irrespective of the
starting point.
d) The product of the width of the seat (Wc) and the length of the seat (Lc) remains the same.
Thus for a given value of seat cushion angle(αc) and backrest angle(αb) the surface area of
the seat cushion remains the same as the pressure acting on the Ischial Tuberosities is
unchanged.
The study of change in design affected by change in αc and αb is carried out in the following
section.
1.8. Parametric Study
Analysis of the behavior of the objective function [Volume of the seat (Vs)] with change in the
four parameters employed in this optimization study would be of particular interest to obtain a
better understanding of the correlation between the design model and the optimum value of Vs.
The parametric study is done separately with respect to the Seat Cushion angle (αc), Backrest
angle (αb) and Pelvis mass value(6)
(Pm) - Torso mass value(6)
(Tm) and the behavior of the width
of the seat (Wc) and the length of the seat (Lc) are also analyzed along with the volume of the
seat (Vs).
Note: The behavior of Lumbar Lordosis angle (θl) is not analyzed for we realized that its value
always remains the same due to active upper bound on the radius of curvature of the Lumbar
Support (Rl)
Parametric Study with respect to the Seat Cushion angle (αc):
Table 6: Parametric Study with respect to the Seat Cushion angle (αc )
αc (deg)*
Wc (mm) Lc (mm) Vs (mm3)
10 549.9741 515.3475 5.022*107
15 549.9541 505.4317 4.9976*107
20 540.5336 500.1982 4.9217*107
25 521.2110 500.2097 4.8251*107
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* For each selection of αc, the value of αb =105 deg and the values of Pm ,Tm are 0.2997, 0.3092
respectively and the starting points of the design variables are same as in the Numerical Analysis
section.
From the parametric study with respect to the seat cushion angle (αc), it can be realized that with
the increase in the seat cushion angle, there is a decrease in the values of the width of the seat
(Wc), length of the seat (Lc) and the volume of the seat (Vs). This behavior is along the expected
lines as Wc and Lc are related to αc by the cosine of the angle, as expressed in the constraint g20,
which is an active constraint. Thus with the increase in the value of αc , its cosine component
decreases (as αc ≤ 90 deg) and subsequently the values of Wc and Lc decrease to maintain the
equality at the active constraint. Consequently the volume of the seat (Vs) increases.
With the decrease in the seat cushion angle, the pressure in the region of Ischial
Tuberosities (Pit) increases. Hence the practical application of this parametric study would
involve modification in the structural construction of the seat cushion (with decreasing αc) such
that there is a better distribution of the pressure over the surface of the cushion, thus decreasing
the peak pressure at Ischial Tuberosities (and consequently decreasing the discomfort).
Parametric Study with respect to the Backrest angle (αb):
Table 7: Parametric Study with respect to the backrest angle (αb )
αb (deg)*
Wc (mm) Lc (mm) Vs (mm3)
105 521.2110 500.2097 4.8251*107
110 521.2110 500.2097 4.8251*107
115 521.2110 500.2097 4.8251*107
120 521.2110 500.2097 4.8251*107
* For each selection of αb, the value of αc =10 deg and the values of Pm ,Tm are 0.2997, 0.3092
respectively and the starting points of the design variables are same as in the Numerical Analysis
section.
From the parametric study with respect to the backrest angle (αb), it can be realized that with the
increase in the seat cushion angle, there is no change in the values of the width of the seat (Wc),
length of the seat (Lc) and the volume of the seat (Vs). This can be attributed to the generous
nature of the constraint applied to the backrest angle (αb), as expressed by the inactivity of the
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constraint g21. Hence the pressure in the region of Lumbar spine (Pl) would always be in excess
of the constraint value and the level of comfort would not be affected by the change in the value
of the backrest angle (αb).
Parametric Study with respect to Gender [Pelvis mass value(6)
(Pm) - Torso mass value(6)
(Tm)]:
Table 8: Parametric Study with respect to the gender
Gender Pm
Tm
Wc (mm) Lc (mm) Vs (mm3)
Male 0.2997
0.3213
521.2110 500.2097 4.8251*107
Female 0.3157
0.3092
549.0516 500.1962 4.9643*107
* For each selection of gender value of αc =10 deg and the value of αb =105 deg and the starting
points of the design variables are same as in the Numerical Analysis section.
From the parametric study with respect to the gender it can be realized that, when the gender
being accommodated in the seat is changed from male to female, there is an increase in the
values of the length of the seat (Lc) and the volume of the seat (Vs), while the width of the seat
(Wc) remains almost unchanged. This can be attributed to different distribution of body mass
between the pelvis and torso, in men and woman. However as we have realized from the
previous parametric studies that level of discomfort in our construction of optimization problem
is influenced by the pressure in the region of Ischial Tuberosities (Pit) but remains unchanged
with the pressure in the region of Lumbar spine (Pl).
Hence due to greater Pelvis mass value(6)
(Pm) in females than in males, greater pressure
would act in the region of Ischial Tuberosities. This calls for a construction of a seat such that
there is a better distribution of the pressure over the surface of the cushion. This need is
expressed as increase in the cushion surface area (Sc), while in practice the structure of the seat
should be changed to facilitate better pressure distribution, thus reducing discomfort.
1.9. Discussion of Results
Thus the optimization study and the subsequent analysis would recommend the following design
practices to minimize the volume of the seat (Vs):
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1. The decrease in the volume of seat can be affected by the decreasing the values of width of
the backrest at waist (Wbw), width of the backrest at chest (Wbc), Thickness of the cushion
and backrest (T), Radius of curvature of the Thoracic support (Rt) and Thoracic kyphosis
angle (θt), subject to the values of their lower bounds as specified by anthropometric
measurements.
2. The decrease in the volume of seat can be affected by the increasing the value Radius of
curvature of the Lumbar support (Rl), subject to the value of its upper bound as specified by
anthropometric measurements.
3. The decrease in the volume of seat can be achieved by the decreasing the values of the width
of the seat (Wc) and length of the seat (Lc)), subject to the lower constraint on the support
parameter – the height of the apex of the Lumbar Support.
4. The decrease in the volume of seat also results from the decrease in the values of the
Lumbar Lordosis angle (θt), subjected to the upper constraint applied on the pressure at the
Ischial Tuberosities (Pit).
These recommendations are not restricted to any particular anthropmetric percentile of human
population, as they have been constructed by providing implicit weight age to the design variable
causing most discomfort to a human occupant classified under any segment of anthropometric
data. Thus in the design for the width of the seat the hip dimensions of 95th percentile female
population is considered while for the radius of curvature of the Lumbar support, the Lumbar
vertebral measurement of the 95th
percentile male population is considered. Hence the
recommendations yield a seat design that imparts generic comfort to the human population.
Simultaneous implementation of the above mentioned design recommendations would minimize
the volume of the seat (Vs), which attains a value of 4.8251*107
mm3 at the following values of
the design variables (in respective units).
Table 9: Values of the design variables at the solution
Lc Wc Wbw Wbc T Rl Rt θl θt
Value at
the
solution
521.2110 500.2097 360 456 100 460 460 51.4054 20
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2. SUBSYSTEM OPTIMIZATION: SEAT SAFETY (BALAJI RAMANATHAN)
2.1. Introduction
Occupant Safety is one of the factors which cannot be compromised during the process of
development of a new vehicle platform. One of the critical tests performed over the vehicle is the
frontal crash test. Typically, this test involves a fully occupational vehicle with a Hybrid III
dummy placed in the driver position. The main parameters noted from the test are Head Injury
Criterion (HIC), Head and Knee excursions, Chest deflection and pelvis acceleration. Ideally,
minimization of these parameters is a multi-objective problem. However in this work, the chest
deflection and pelvis acceleration values are neglected. The head and knee excursion values are
placed as constraints and the single objective remains the Head Injury Criterion.
2.2. Problem Statement and Definitions
The objective of the optimization problem is to minimize the head injury criterion within
allowable limits of head and knee excursion values. The variables of the minimization problem
are the positions of the anchorage points of a three-point seat belt system which is a passive
safety device used to minimize injury levels of the occupants in case of an accident. The three
anchorage points of the three-point seat belt are anchor point, buckle point and D-ring point. The
graphical representation of these three points is shown in the figure below.
Figure 8: Three-point seatbelt
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The head injury criterion is a measure of the likelihood of head injury arising from an impact.
The variable is derived from the acceleration/time history of an accelerometer mounted at the
center of gravity of a dummy’s head, when the dummy is exposed to crash forces.
𝐻𝐼𝐶 = 1
𝑡2 − 𝑡1. 𝑎𝑑𝑡
𝑡2
𝑡1
2.5
. (𝑡2 − 𝑡1)
𝑚𝑎𝑥
where 𝑡1 and 𝑡2 are the initial and final times (in seconds) of the interval during which HIC
attains a maximum value, and acceleration is measured in g’s. It should also be noted that the
maximum time duration, 𝑡2 − 𝑡1, is limited to a specific value, usually and in this work to 15 ms.
Head excursion is a measure of the maximum distance travelled by the center of gravity of the
head from its initial position. Similarly, knee excursion is a measure of the maximum distance
travelled by the knee joint from its initial position. In this work, the head and knee excursions are
measured in the longitudinal direction of the vehicle co-ordinate system (i.e.) forward
movement.
2.3. Range of Motion of the Anchorage Points
The allowable limits for the positioning of the anchorage points of the seat belt are taken as
prescribed in Reed et al.1 with the H-point of the Anthropomorphic Test Dummy (ATD) taken as
the origin, X-axis is positive forward, Y-axis is positive to the right when viewed from front and
Z-axis is positive upward. The prescribed values are transformed by moving the origin of co-
ordinate system of measurement to the seat reference point (SgRP) of the seat. The bounds of the
three points with respect to the seat reference point (SgRP) are mentioned in the table below. All
the dimensions mentioned are in meters.
Table 10: Upper and Lower bounds of variables
Point Component Lower Bound Upper Bound
Anchor
X -0.194 -0.007
Y -0.2
Z -0.01
Buckle
X -0.125 0.007
Y 0.25
Z 0.04
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D-ring
X -0.5 -0.198
Y -0.292 -0.194
Z 0.524 0.668
2.4. Nomenclature
It can be seen from the above table that the number of variables in the system is five. There are
some parameters in the system which interact with the other subsystems – seat back angle and
seat cushion angle to name a few. The detailed list of variables, parameters and their notation are
listed in the table below.
Table 11: Nomenclature of Seat Belt Anchorage Point Positions
S. No. Notation Unit Type Description
1 f NA Objective Head Injury Criterion
2 g1 m Constraint Head Excursion
3 g2 m Constraint Knee Excursion
4 x1 m Variable Anchor point X position w.r.t. SgRP
5 x2 m Variable Buckle point X position w.r.t. SgRP
6 x3 m Variable D-ring point X position w.r.t. SgRP
7 x4 m Variable D-ring point Y position w.r.t. SgRP
8 x5 m Variable D-ring point Z position w.r.t. SgRP
9 a1 deg Parameter Seat Back Angle w.r.t. vertical
10 a2 deg Parameter Seat Cushion Angle w.r.t. horizontal
11 L1 m Parameter Seat Back Length
12 L2 m Parameter Seat Cushion Length
13 W1 m Parameter Width of Seat Cushion
14 W2 m Parameter Width of Seat Back
2.5. Procedure Setup
The crash test is simulated in MADYMO software environment. A standard FMVSS pulse is
used to evaluate the occupant kinematics as seen in figure 2. Even though the pulse is defined for
200 ms, the test is conducted only for 120 ms as the dominant part of the pulse ends at 100 ms
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and rebound starts thereafter. The seat back and cushion angles are set to 20 degrees and 15
degrees from the vertical and horizontal respectively. The buckle point is set to be to the left of
the occupant when viewed from front which corresponds to a driver in countries like UK or India
or to a front seat passenger in the USA. However, the dummy is perfectly symmetric about the
sagittal plane and hence it the simulation also corresponds to a driver in the USA.
A Hybrid III 50th percentile male dummy as available in the MADYMO database is used across
the simulations. For every set of values of the anchorage points’ positions, belt-fitting has to be
performed to adapt the natural path of the seat belt. Hence, a pre-simulation is performed every
time before the main simulation is performed. A Python code was written and is used to read the
seat belt data and the end of the pre-simulation run and use that seat belt data for the actual crash
simulation. This linking is possible as most of MADYMO’s inputs and outputs are ASCII
readable.
There are some known limitations in the design of this particular procedure setup. In reality, the
airbag deploys within the first few milliseconds of crash. In this particular setup, the airbag has
been neglected. The MADYMO dummy is modeled out of ellipsoids which may not represent
the actual geometry of a 50th
percentile male American. However, given the scope of this
particular work is anchorage points positioning, the comparative results should be valid enough
to select the optimal position of the anchorage points.
2.6. Design of Experiments
The relation between the given variables, the objective and constraints in this given problem is
quite complicated when computed analytically and at times, practically impossible. Hence, a
meta-model relationship between the variables, objective and the constraint has to be developed.
For this purpose, DOE points were extracted and a second-order curve fitting was used.
modeFrontier, a commercial multi-objective optimization and design software was used for these
processes.
A total of 500 data points were generated using Uniform Latin Hypercube method. These data
points were fed into the MADYMO environment through integration with modeFrontier. The
workflow is shown in figure 3. Each iteration took close to a minute and up to three parallel
iterations were allowed. In total, it took 3 hours to generate the entire test matrix. The R-square
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values of the data fitting processes are 0.9771, 0.9695 and 0.9693 respectively for HIC, head
excursion and knee excursion respectively and are acceptable.
2.7. Mathematical Model
The mathematical expression for HIC, head excursion and knee excursion in terms of the given
variables as a second order polynomial can be given as follows.
𝑓 = −377.557 + 299.884𝑥1 + 1507.444𝑥2 + 805.908𝑥3 − 3882.742𝑥4
+ 858.493𝑥5 − 128.598𝑥12 − 1347.607𝑥1𝑥2 + 264.933𝑥2
2 − 138.8𝑥1𝑥3
− 74.633𝑥2𝑥3 + 2305.629𝑥32 + 178.824𝑥1𝑥4 + 387.882𝑥2𝑥4 − 3610.233𝑥3𝑥4
+ 1623.466𝑥42 − 851.659𝑥1𝑥5 − 4041.634𝑥2𝑥5 + 483.056𝑥2𝑥5
+ 5205.753𝑥4𝑥5 + 642.869𝑥52
𝑔1 = 0.237 + 0.022𝑥1 + 0.122𝑥2 + 0.176𝑥3 − 1.106𝑥4 − 0.364𝑥5 + 0.071𝑥12
+ 0.378𝑥1𝑥2 + 1.082𝑥22 + 0.054𝑥1𝑥3 + 0.329𝑥2𝑥3 + 0.688𝑥3
2 − 0.052𝑥1𝑥4
− 0.378𝑥2𝑥4 − 1.269𝑥3𝑥4 + 0.414𝑥42 + 0.093𝑥1𝑥5 − 0.032𝑥2𝑥5 + 0.222𝑥2𝑥5
+ 0.697𝑥4𝑥5 + 0.504𝑥52
𝑔2 = 0.218 + 0.029𝑥1 + 0.166𝑥2 + 0.172𝑥3 − 1.109𝑥4 − 0.418𝑥5 + 0.085𝑥12
+ 0.404𝑥1𝑥2 + 1.101𝑥22 + 0.060𝑥1𝑥3 + 0.320𝑥2𝑥3 + 0.690𝑥3
2 − 0.087𝑥1𝑥4
− 0.426𝑥2𝑥4 − 1.280𝑥3𝑥4 + 0.477𝑥42 + 0.072𝑥1𝑥5 − 0.133𝑥2𝑥5 + 0.226𝑥2𝑥5
+ 0.741𝑥4𝑥5 + 0.557𝑥52
Let us assume that the safe excursion limits before the occupant hits any part of the car in front
of him/her is 25 cm. Then, the head excursion and knee excursion values can be capped at 0.25m
and 0.25m respectively. However, it is evident that if both the values of excursion are set to the
same upper cap value, the knee excursion constraint is going to be dominated by head excursion
constraint as the head has more options for movement because of the rotation about the hip. So,
the knee excursion constraint can be capped at a more stringent value, say 20 cm, considering
safety factor of 5 cm. Hence, the constraints can be written in negative form as follows.
𝑔1 − 0.250 ≤ 0
𝑔2 − 0.200 ≤ 0
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2.8. Model Analysis
The table below shows a monotonicity analysis of the objective and the constraint functions in
the given bound of the variables.
Table 12: Monotonicity Analysis
𝑥1 𝑥2 𝑥3 𝑥4 𝑥5
𝑓 - - * - +
𝑔1 + * * - *
𝑔2 + * * - *
* varying monotonicity (descent and then uphill with increase in variable)
It can be seen from the monotonicity analysis table that the optimal value of 𝑥4 is set at its upper
bound. However, the behaviors of the other variables are not evident from the analysis. It can
also be observed that the two constraints have the same behavior with respect to the variables. It
can be possible that one of the constraints is dominant over the other over the entire domain of
operation of the variables. However, the data points of the DOE study do not indicate any such
dominance.
2.9. Numerical Analysis
The above defined mathematical model of the objective function and constraints were input to
MATLAB for optimization. Sequential Quadratic Programming (SQP) method was used for
optimization by the use of ‘fmincon’ function. The code is given in appendix and the output
given by MATLAB is as follows.
𝑥∗ = −0.0893 0.007 − 0.3858 − 0.194 0.524 → (𝐾𝐾𝑇 𝑝𝑜𝑖𝑛𝑡)
𝑓∗ = 204.9787
𝑔1∗ − 0.25 = −0.016 & 𝑔2∗ − 0.20 = 0.0
𝑒𝑥𝑖𝑡 𝑓𝑙𝑎𝑔 = 5 (∆𝑓 < 𝑡𝑜𝑙𝑒𝑟𝑎𝑛𝑐𝑒)
It can be seen from the above result that 𝑔2 i.e. the knee excursion is an active constraint and
hence an equality constraint at the solution. The corresponding output as delivered by
MADYMO for 𝑥∗ is as follows.
𝑓∗ = 208.98
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𝑔1∗ − 0.25 = −0.0010 & 𝑔2∗ − 0.20 = 0.0002
HIC value of 208.98 is very much acceptable. In fact, most of the HIC values obtained in the
DOE were below 560 (a suggested limit)2 and are acceptable. This is because the bounds to these
variables are selected as prescribed by Reed et al. based on statistical data and some laboratory
measurements.
2.10. Parametric Study –Constraint Cap Study
A parametric study was conducted to evaluate the variation in the objective function with respect
to variations in the constraints. The results are as follows.
First, the knee excursion cap was relaxed to 0.25m. The results obtained were as follows.
𝑥∗ = −0.007 0.007 − 0.3816 − 0.194 0.524 → (𝐾𝐾𝑇 𝑝𝑜𝑖𝑛𝑡)
𝑓∗ = 194.6857
𝑔1∗ − 0.25 = −0.0614 & 𝑔2∗ − 0.25 = −0.0454
𝑒𝑥𝑖𝑡 𝑓𝑙𝑎𝑔 = 5 (∆𝑓 < 𝑡𝑜𝑙𝑒𝑟𝑎𝑛𝑐𝑒)
It can be observed that both the constraints are inactive at the solution and four of five variables
are controlled by bounds. The variable 𝑥3 is determined by the unconstrained minimum of the
objective function after fixing the values of the other variables at its optimal values (bounds),
provided it satisfies the constraints also. It can also be noted that if the knee excursion cap is
placed anywhere above 0.2046m, it turns inactive. The corresponding MADYMO output is as
follows.
𝑓∗ = 196.11
𝑔1∗ − 0.25 = −0.0647 & 𝑔2∗ − 0.25 = −0.0408
Second, the knee excursion cap was restricted to 0.15m. The solution did not converge as there
was no feasible solution. The knee excursion cap was relaxed slightly from its new cap value of
0.15m until a value of 0.193cm when a feasible solution was found as follows.
𝑥∗ = −0.194 0.007 − 0.3941 − 0.194 0.5883 → (𝐾𝐾𝑇 𝑝𝑜𝑖𝑛𝑡)
𝑓∗ = 248.3958
𝑔1∗ − 0.25 = −0.0233 & 𝑔2∗ − 0.193 = 0.0
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𝑒𝑥𝑖𝑡 𝑓𝑙𝑎𝑔 = 5 (∆𝑓 < 𝑡𝑜𝑙𝑒𝑟𝑎𝑛𝑐𝑒)
The corresponding MADYMO output is as follows.
𝑓∗ = 252.18
𝑔1∗ − 0.25 = −0.0201 & 𝑔2∗ − 0.193 = −0.0001
From the above result, it can be seen that by changing the knee constraint cap between 19.3cm
and 20.46cm, the HIC value reduces from 252.18 to 196.11 drastically. As mentioned before, the
actual problem is a multi-objective problem and the trade-off to slightly increase the knee
excursion cap to achieve a considerable reduction in HIC value is arguable. In all these cases, the
head excursion was within limits and can be maintained the same.
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3. SYSTEM INTEGRATION
3.1. Problem Statement
The task of system integration poses a unique challenge primarily on two accounts:
a. The sub system level objectives deal with quantities that cannot be coalesced into a single
objective function because of dealing with disparate entities like the volume of the seat and
the Head Injury Criterion.
b. The tedium involved in computing the Head Injury Criterion at each value of the Seat
Cushion Angle (αc).
Thus we seek to adopt an integration scheme that incorporates the subsystem level objectives of
the ‘Seat Comfort’ and ‘Seat Safety’, with minimal level of tradeoffs. The subsystems interact
through the seat cushion angle (αc) and the backrest angle (αb), with these angles serving as
parameters for both the subsystems. With regard to the ‘Seat Comfort” subsystem the increase in
the seat cushion angle (αc) affects a decrease in the volume of seat (Vs) while the backrest angle
(αb) does not affect the volume of the seat with its increase of decrease within the feasible space.
However such a study of the Head Injury Criterion with the change in the seat adjustment angles
does not figure in the ‘Seat Safety’ subsystem. Further, the coefficients associated with the
mathematical representation of the Head Injury Criterion differ from one value of the seat
adjustment angles to other. Hence the prediction of the change in Head Injury Criterion with the
change in seat adjustment angles at any set value of seat adjustment angles would be infeasible.
Thus, the search for an optimal solution is formulated as a multi objective problem involving
minimization of the volume of the seat (Vs) and the Head Injury Criterion. The investigation of
the optimal solution for this multi objective problem is conducted at discrete points in the
feasible design space of the seat cushion angle (αc). The choice of this optimization scheme is
consequence of the following observations:
a. The tedium associated with the computation of the Head Injury Criterion and its input as a
parameter would render the study of the entire feasible design space of the seat adjustment
angles practically infeasible.
b. The change in the backrest angle (αb) affects the Head Injury Criterion but does not affect
the volume of the seat (Vs). Thus in order to facilitate a study over a considerable number of
reference points of significance, the backrest angle (αb) is held fixed, while the seat cushion
angle (αc) is varied through discrete points in its feasible design space.
Note: In this regard, a reference point of significance is one which affects change in both
the volume of the seat (Vs) and the Head Injury Criterion.
Thus in this design scheme the optimum value of the Head Injury Criterion may be compromised
owing to the backrest angle (αb) being held fixed. But this trade off is essential for a
comprehensive analysis of the entire system (within a reasonable allotment of time).
ME 555-10-07 Final Project Report
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Further the design space of the seat cushion angle (αc), for the purpose of study is restricted to
the integer values of αc from 15 deg to 25 deg. This decision on the domain of αc is arrived upon
by establishing a maximum permissible limit of 4 % on the change in the volume of seat from its
subsystem level minimum volume of 4.8251*107
mm3
and its necessity is again dictated by the
desire to limit the tediousness of the Head Injury Criterion calculation without losing data points
of significance. Although this design preference can be satisfactorily be applied with regard to
change in Vs, the robustness of the design preference needs to verified by the observed change in
the value of Head Injury Criterion. The robustness of the design preference is validated if the
value of Head Injury Criterion at the system level optimum is also within reasonably small
deviation from its subsystem level optimal value, as realized in the subsequent section.
3.2. Nomenclature Table 13: Nomenclature used in the system model
Index Symbol Description Unit
1 αc Seat cushion angle degrees
2 αb Backrest angle degrees
3 Cs Scale factor for seating area calculation 1
4 Cit Scale factor for pressure at Ischial Tuberosities 1
5 Cl Scale factor for pressure at Lumbar spine 1
6 g Acceleration due to gravity m/s2
7 H H-point 1
8 Hl Lumbar height mm
9 Lb Length of the backrest mm
10 Lc Length of the cushion mm
11 M Mass of the human occupant kg
12 Pit Pressure at the Ischial Tuberosities N/ mm2
13 Pl Pressure at the Lumbar spine N/mm2
14 Pm Pelvis mass value 1
15 Rl Radius of curvature of the Lumbar support mm
16 Rt Radius of curvature of the Thoracic support mm
17 Sc Surface area of the cushion mm2
18 Sl Surface area of the Lumbar support section mm2
19 Ss Seating Surface area mm2
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20 T Thickness of the cushion and backrest mm
21 Tm Torso mass value 1
22 θl Lumbar Lordosis angle degrees
23 θt Thoracic Kyphosis angle degrees
24 Vbc Volume of the backrest at chest or upper back mm3
25 Vbw Volume of the backrest at waist or lower back mm3
26 Vc Volume of the cushion mm3
27 Vs Volume of the seat mm3
28 Wbc Width of the backrest at chest or upper back mm
29 Wbw Width of the backrest at waist or lower back mm
30 Wc Width of the cushion mm
31 x1 Anchor point X position w.r.t. SgRP m
32 x2 Buckle point X position w.r.t. SgRP m
33 x3 D-ring point X position w.r.t. SgRP m
34 x4 D-ring point Y position w.r.t. SgRP m
35 x5 D-ring point Z position w.r.t. SgRP m
3.3. Mathematical Model
Objective function
The objective of the integrated system is to minimize the volume of the seat (Vs) and the Head
Injury Criterion, under the requirements of fit, feel, support constraints as well as head and knee
excursion criteria. Thus the system objective is modeled as a multi objective problem and these
objectives may be competing with decreasing Head Injury Criterion increasing the volume of the
seat or vice versa (as subsequently realized).
Objective Function
Minimize 𝑓 = 𝑓1
𝑓2
𝑓1 = 𝑉𝑠 = 𝐿𝑐𝑊𝑐𝑇𝑐 + 𝑊𝑏𝑤. 𝜋. 𝜃𝑙
360 𝑅𝑙 +
𝑇
2
2
− 𝑅𝑙 −𝑇
2
2
+ 𝑊𝑏𝑐. 𝜋. 𝜃𝑡
360 𝑅𝑡 +
𝑇
2
2
− 𝑅𝑡 −𝑇
2
2
and
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𝑓2 = 𝐻𝐼𝐶 = 𝐶0 + 𝐶1𝑥1 + 𝐶2𝑥2 + 𝐶3𝑥3 + 𝐶4𝑥4 + 𝐶5𝑥5 + 𝐶11𝑥12 + 𝐶12𝑥1𝑥2 + 𝐶22𝑥2
2 + 𝐶13𝑥1𝑥3 + 𝐶23𝑥2𝑥3
+ 𝐶33𝑥32 + 𝐶14𝑥1𝑥4 + 𝐶24𝑥2𝑥4 + 𝐶34𝑥3𝑥4 + 𝐶44𝑥4
2 + 𝐶15𝑥1𝑥5 + 𝐶25𝑥2𝑥5 + 𝐶35𝑥2𝑥5
+ 𝐶45𝑥4𝑥5 + 𝐶55𝑥52
where C0, C1…C55 are the second order polynomial curve fitting coefficients of HIC.
Constraints
The system level constraint set is the unified set of constraint sets of the sub system level
constraints as briefly described below:
1. The constraints for the ‘Seat Comfort’ subsystem are mainly categorized as the fit,
support and feel constraints.
2. The constraints for the ‘Seat Safety’ subsystem are the Head Excursion and Knee
Excursion criteria apart from bounds on selected coordinates of anchor point, buckle
point and D-ring point.
Design Variables, Parameters and Constants:
Table 14: Design variables, parameters and constants
Symbol Description Type
Lc Length of the cushion Variable
Wc Width of the cushion Variable
Wbw Width of the backrest at waist or lower back Variable
Wbc Width of the backrest at chest or upper back Variable
T Thickness of the cushion and backrest Variable
Rl Radius of curvature of the Lumbar support Variable
Rt Radius of curvature of the Thoracic support Variable
θl Lumbar Lordosis angle Variable
θt Thoracic Kyphosis angle Variable
x1 Anchor point X position w.r.t. SgRP Variable
x2 Buckle point X position w.r.t. SgRP Variable
x3 D-ring point X position w.r.t. SgRP Variable
x4 D-ring point Y position w.r.t. SgRP Variable
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x5 D-ring point Z position w.r.t. SgRP Variable
αc Seat cushion angle Parameter
αb Backrest angle Parameter
Pm Pelvis mass value Parameter
Tm Torso mass value Parameter
M Mass of the human occupant Parameter
Cs Scale factor for seating area calculation Parameter
Cit Scale factor for pressure at Ischial Tuberosities Parameter
Cl Scale factor for pressure at Lumbar spine Parameter
g Acceleration due to gravity Constant
The values of the parameters and constants employed in this study are as follows:
Parameters:
Seat Cushion angle (αc) = [15,16,17,18,19,20,21,22,23,24,25] deg.
Backrest angle (αb) = 110 deg.
The Pelvis mass value(6)
(Pm) = 0.2997 (for men)
0.3157 (for women)
The Torso mass value(6)
(Tm) = 0.3213 (for men)
0.3092 (for women)
Constants:
Mass of the Human Occupant (M) = 70 kg
The scale factor of seating area calculation (Cs) = (432/500)
The scale factor for pressure at Ischial Tuberosities(5)
(Cit) = 3.624
The scale factor for pressure at Lumbar Spine(7)
(Cl) = 0.719
The acceleration due to gravity (g) = 9.8 m/s2
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Summary Model:
Objective Function
Minimize 𝑓 = 𝑓1
𝑓2
𝑓1 = 𝑉𝑠 = 𝐿𝑐𝑊𝑐𝑇𝑐 + 𝑊𝑏𝑤. 𝜋. 𝜃𝑙
360 𝑅𝑙 +
𝑇
2
2
− 𝑅𝑙 −𝑇
2
2
+ 𝑊𝑏𝑐. 𝜋. 𝜃𝑡
360 𝑅𝑡 +
𝑇
2
2
− 𝑅𝑡 −𝑇
2
2
and
𝑓2 = 𝐻𝐼𝐶 = 𝐶0 + 𝐶1𝑥1 + 𝐶2𝑥2 + 𝐶3𝑥3 + 𝐶4𝑥4 + 𝐶5𝑥5 + 𝐶11𝑥12 + 𝐶12𝑥1𝑥2 + 𝐶22𝑥2
2 + 𝐶13𝑥1𝑥3 + 𝐶23𝑥2𝑥3
+ 𝐶33𝑥32 + 𝐶14𝑥1𝑥4 + 𝐶24𝑥2𝑥4 + 𝐶34𝑥3𝑥4 + 𝐶44𝑥4
2 + 𝐶15𝑥1𝑥5 + 𝐶25𝑥2𝑥5 + 𝐶35𝑥2𝑥5
+ 𝐶45𝑥4𝑥5 + 𝐶55𝑥52
where C0, C1…C55 are the second order polynomial curve fitting coefficients of HIC.
subject to:
𝑔1 = 440 − 𝐿𝑐 ≤ 0
𝑔2 = 𝐿𝑐 − 550 ≤ 0
𝑔3 = 500 − 𝑊𝑐 ≤ 0
𝑔4 = 360 − 𝑊𝑏𝑤 ≤ 0
𝑔5 = 456 − 𝑊𝑏𝑐 ≤ 0
𝑔6 = 100 − 𝑇 ≤ 0
𝑔7 = 𝑇 − 120 ≤ 0
𝑔8 = 509 − 2𝑅𝑙. 𝑠𝑖𝑛𝜋. 𝜃𝑙
360− 2𝑅𝑡. 𝑠𝑖𝑛
𝜋. 𝜃𝑡
360≤ 0
𝑔9 = 2𝑅𝑙. 𝑠𝑖𝑛𝜋. 𝜃𝑙
360+ 2𝑅𝑡. 𝑠𝑖𝑛
𝜋. 𝜃𝑡
360− 646 ≤ 0
𝑔10 = 400 − 𝑅𝑙 ≤ 0
𝑔11 = 𝑅𝑙 − 460 ≤ 0
𝑔12 = 460 − 𝑅𝑡 ≤ 0
𝑔13 = 𝑅𝑡 − 500 ≤ 0
𝑔14 = 40 − 𝜃𝑙 ≤ 0
𝑔15 = 𝜃𝑙 − 60 ≤ 0
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𝑔16 = 20 − 𝜃𝑡 ≤ 0
𝑔17 = 𝜃𝑡 − 40 ≤ 0
𝑔18 = 200 − 𝑅𝑙. 𝑠𝑖𝑛𝜋. 𝜃𝑙
360≤ 0
𝑔19 = 𝑅𝑙. 𝑠𝑖𝑛𝜋. 𝜃𝑙
360− 250 ≤ 0
𝑔20 = 𝐶𝑖𝑡. 𝑀. 𝑔. 𝑃𝑚. 𝑐𝑜𝑠 𝜋.𝛼𝑐
180 / 𝐶𝑠. 𝐿𝑐. 𝑊𝑐 – (3𝑒 − 3) ≤ 0
𝑔21 = 2.5𝑒 − 3 − 𝐶𝑙. 𝑀. 𝑔. 𝑇𝑚. 𝑐𝑜𝑠(𝜋.180 − 𝛼𝑏
180)/ 2𝜋. 𝜃𝑙. 𝑊𝑏𝑤. (𝑅𝑙 +
𝑇
2)/360 ≤ 0
𝑔22 = 𝐶0 + 𝐶1𝑥1 + 𝐶2𝑥2 + 𝐶3𝑥3 + 𝐶4𝑥4 + 𝐶5𝑥5 + 𝐶11𝑥12 + 𝐶12𝑥1𝑥2 + 𝐶22𝑥2
2 + 𝐶13𝑥1𝑥3
+ 𝐶23𝑥2𝑥3 + 𝐶33𝑥32 + 𝐶14𝑥1𝑥4 + 𝐶24𝑥2𝑥4 + 𝐶34𝑥3𝑥4 + 𝐶44𝑥4
2 + 𝐶15𝑥1𝑥5 + 𝐶25𝑥2𝑥5
+ 𝐶35𝑥2𝑥5 + 𝐶45𝑥4𝑥5 + 𝐶55𝑥52 − 0.25 ≤ 0
where C0, C1…C55 the second order polynomial curve fitting coefficients of Head Excursion.
𝑔23 = 𝐶0 + 𝐶1𝑥1 + 𝐶2𝑥2 + 𝐶3𝑥3 + 𝐶4𝑥4 + 𝐶5𝑥5 + 𝐶11𝑥12 + 𝐶12𝑥1𝑥2 + 𝐶22𝑥2
2 + 𝐶13𝑥1𝑥3
+ 𝐶23𝑥2𝑥3 + 𝐶33𝑥32 + 𝐶14𝑥1𝑥4 + 𝐶24𝑥2𝑥4 + 𝐶34𝑥3𝑥4 + 𝐶44𝑥4
2 + 𝐶15𝑥1𝑥5 + 𝐶25𝑥2𝑥5
+ 𝐶35𝑥2𝑥5 + 𝐶45𝑥4𝑥5 + 𝐶55𝑥52 − 0.20 ≤ 0
where C0, C1…C55 the second order polynomial curve fitting coefficients of Knee Excursion
Set Constraints:
Lc, Wc, Wbw,Wbc, T, Rl, Rt ≥ 0
θl, θt ≥ 0 deg; θl, θt≤ 90 deg
3.4. Numerical Results
The system level optimization (for calculation of Pareto optimal points) is carried out through an
iterative procedure by Sequential Quadratic Programming (with Quasi Newton Hessian update)
as supported by the ‘fmincon’ solver of the optimization toolbox of MATLAB and HIC
verification from MADYMO.
The Pareto set of optimal points for the selected values of the seat cushion angles (αc) are plotted
to realize the interaction between the seemingly contesting objectives of the volume of the seat
ME 555-10-07 Final Project Report
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(Vs) and the Head Injury Criterion (from MADYMO). The behaviour of the individual objectives
is plotted in Figure 9 and Figure 10
Figure 9: Variation of Seat Volume with Seat Cushion Angle
Figure 10: Variation of HIC with Seat Cushion Angle
From these plots it can be realized that the volume of the seat (Vs) decreases with the increase in
the seat cushion angle (αc) over the set of selected values. However the Head Injury Criterion is
observed to decrease with the increase in the seat cushion angle (αc) from 15 deg to 19 deg and
4.80E+07
4.82E+07
4.84E+07
4.86E+07
4.88E+07
4.90E+07
4.92E+07
4.94E+07
4.96E+07
4.98E+07
5.00E+07
15 17 19 21 23 25
Seat
Vo
lum
e, m
m3
Seat Cushion Angle (from horizontal), deg
195
200
205
210
215
220
225
230
235
240
15 17 19 21 23 25
Min
imal
He
ad In
jury
Cri
teri
on
, no
un
it
Seat Cushion Angle (from horizontal), deg
ME 555-10-07 Final Project Report
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subsequently increases with increasing value of αc. Thus on the basis of this observed behaviour
we evaluate the volume of seat (Vs) at the seat cushion angle (αc) of 19 deg and realize that the
value obtained (Vs = 4.9385*107 mm3) is within 2.5% of the subsystem level optimum value of Vs (Vs =
4.8251 *107 mm3). This deviation of the volume of seat (Vs) is thus acceptable to predefined design
preferences and the Pareto Optimal point – Vs = 4.9385*107 mm3 and Head Injury Criterion =
197.64 (no unit) – is chosen as the optimum value of the multi objective problem.
Figure 11: Pareto Curve for the bi-criterion problem (HIC vs. Seat Volume)
The coefficients of the Head Injury Criterion and the head and knee excursions at the optimal
point (seat back angle = 19 degrees) are as follows.
Table 15: Coefficients of the second order curve fitted for HIC, Head and Knee Excursions (αc = 19 deg)
Coefficient f2 g22 g23
C0 -347.387 0.698 0.639
C1 613.625 -0.200 -0.211
C2 1142.132 0.109 0.128
C3 764.298 0.214 0.204
C4 -3387.370 -0.713 -0.717
C5 916.005 -1.825 -1.747
C11 1271.920 0.680 0.738
C12 69.774 1.529 1.567
C22 -1130.387 1.249 1.260
195
200
205
210
215
220
225
230
235
240
4.80E+07 4.85E+07 4.90E+07 4.95E+07 5.00E+07
Min
imal
He
ad In
jury
Cri
teri
on
, no
un
it
Seat Volume, mm3
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C13 -255.064 0.056 0.116
C23 -892.002 0.071 0.102
C33 2364.759 0.737 0.726
C14 21.402 0.763 0.655
C24 1066.676 0.866 0.799
C34 -2882.054 -1.505 -1.517
C44 -347.098 1.633 1.633
C15 -855.779 1.011 1.025
C25 -3210.646 0.604 0.531
C35 895.712 0.116 0.120
C45 3138.135 1.132 1.134
C55 326.822 1.861 1.799
The values of the design variables at the local optimum are
Table 16: Values of the design variables at the solution
Lc Wc Wbw Wbc T Rl Rt θl θt
𝑥∗ 543.90 500.20 360 456 100 460 460 51.41 20
x1 x2 x3 x4 x5
𝑥∗ -0.102 0.007 -0.383 -0.194 0.524
3.5. Discussion of Results
Hence at the system level optimum the Head Injury Criterion (197.64, no unit) attains its
minimum value over the selected set of values of the seat cushion angles (αc),while the volume
of the seat (Vs = 4.9385*107 mm
3) deviates from its minimum value over the selected set of
values of the seat cushion angles (αc) by 2.5%. This satisfies the previously established design
preferences of the volume of the seat (Vs) to lie within 4% from its subsystem level minimum
volume of 4.8251*107
mm3. Hence, these values of volume of the seat (Vs) and Head Injury
Criterion can be considered as optimum values for the integrated system (without further
revising the design preferences).
ME 555-10-07 Final Project Report
47
4. REFERENCES
1. Passenger Car Dimension Definitions – SAE J1100 (UMTRI-29721 A01).
2. Matthew P. Reed, Lawrence W. Schneider, Leda L. Ricci, Survey of Auto Seat Design
Recommendations for Improved Comfort (UMTRI 94-6).
3. Automotive Ergonomics edited by Brian Peacock and Waldemar Karwowski,( Taylor
and Francis).
4. http://www.spineuniverse.com/anatomy/spinal-curves
5. Human Factors in 2000: Driving, Lighting, Seating Comfort, and Harmony in Vehicle
Systems (SP – 1539).
6. Don B. Chaffin, Gunnar B.J. Andersson, Bernard J. Martin, Occupational
Biomechanics, 4th Edition.
7. Human Factors in Driving, Vehicle Seating and Rear Vision (SP-1358)
8. Assessing Child Belt Fit, Volume 1: Effects of Vehicle Seat and Belt Geometry on
Belt Fit for Children with and without Belt positioning Booster seats, Matthew P.
Reed, Sheila M. Ebert-Hamilton, Kathleen D. Klinich, Miriam A. Manary, Jonathan
D. Rupp, UMTRI Sep 08
9. http://www.iihs.org/ratings/protocols/pdf/measures_frontal.pdf