AN IMPROVED NORMALIZATION METHODOLOGY FOR DEVELOPING MEAN HUMAN RESPONSE CURVES
Kevin Moorhouse National Highway Traffic Safety Administration United States Paper Number 13-0192 response curves should prove useful in more accurately characterizing the target human response ABSTRACT to aid in the design of more biofidelic dummies.
Mean human response curves and associated INTRODUCTION biomechanical response targets are commonly developed from Post-Mortem Human Subject Biomechanical response corridors developed from (PMHS) test data to guide the design of human subject test data are commonly used to guide anthropomorphic test devices (ATDs) by providing the design of anthropomorphic test devices (ATDs) “target” biomechanical responses to impact. Since by providing “target” biomechanical responses to differences in anthropometry and physical impact. The biomechanical responses typically characteristics within a group of PMHS can result in consist of physical measures such as force, widely varying response data, the first step in acceleration, or deflection, and could be in the time- developing target biomechanical responses is domain or another domain (e.g., force-deflection). typically to normalize the responses to a certain The ability of an ATD to match these target “standard” anthropometry representing the ATD to responses defines its biofidelity. be designed or evaluated. The normalization procedure should adjust the response data to account The target responses are most often developed by for the variation in anthropometry and physical subjecting a group of Post-Mortem Human Subjects characteristics, and thus should collapse the group of (PMHS) to an impact or crash scenario, measuring curves closer to a single response so that a mean the resulting responses, and then representing each response can be more accurately established that group of responses such that it characterizes the represents the human response of the “standard” response of the selected population and can be used anthropometry selected. Several methods for to evaluate the biofidelity of the corresponding ATD normalizing PMHS test data can be found in the response. One way to accomplish this is to literature, but there is no consensus as to which is the encompass the entire group of response curves for a most effective. In this study, the two most common given measurement using straight-line segment existing normalization techniques, as well as some corridors, and then a biofidelic dummy response is newly developed methodologies, were evaluated by expected to lie entirely within that corridor applying them to both a side impact PMHS sled test (ISO/TR9790, 1999; Lobdell et al., 1973). Another data set, and a lateral and oblique pendulum side methodology is to reduce the group of responses into impact PMHS data set. The efficacy of the a single mean response curve, which itself represents normalization techniques were assessed for each the ATD design target (Cavanaugh et al., 1986; group of common signals by calculating the average Maltese et al., 2002; Morgan et al., 1986). In percent coefficient of variation (%CV) for time- addition to the mean response curve, standard history curves, and an analogous measure for force- deviation curves can be created around the mean to provide both a visual measure of the variation in the deflection curves (%CVellipse). Both of these measures provide a quantifiable assessment of the group of PMHS, as well as a quantitative measure of similitude of the group of curves (i.e., the that variation for assessing the biofidelity of an ATD. normalization technique resulting in the lowest Generally the standard deviation curves envelop the mean curve more tightly than the straight-line average %CV value or %CVellipse value most effectively collapses the curves). The normalization segment corridors, and there is no requirement that a technique found to consistently perform the best is a biofidelic ATD response must lie completely within newly developed extension of impulse momentum- the standard deviation curves. Representing the based normalization in which the stiffness ratio was target response using the mean response and standard determined from effective stiffness values calculated deviation curves is more appealing than straight-line from the test data, rather than using characteristic segment corridors because it provides a quantifiable lengths. Utilization of an improved normalization framework for assessing the biofidelity of an ATD methodology in the development of mean human
Moorhouse 1 while maintaining the shape and characteristics of the Pelvis Force vs Time actual human response to impact. 9000
8000 Since there are a variety of ATDs, each representing 7000 a certain “standard” anthropometry or set of physical characteristics (i.e., 50th percentile male, 5th 6000 percentile female, etc.), it is important that the PMHS 5000 responses used to develop the design targets represent 4000 the same respective population. However, in reality (N) Force 3000 there is often large variation in the physical characteristics within a group of human subjects 2000 (e.g., size, shape, inertial properties, etc.) which 1000 results in widely varying response data. 0
Normalization is a procedure for mathematically -10 0 10 20 30 40 50 60 adjusting the response data to account for the Ti me (ms) variation in physical characteristics, and is often the first step in developing target biomechanical Figure 1. Mean curve resulting from two out-of-phase responses. Successful normalization should collapse responses the group of curves closer to a single response so that a mean response can be more accurately established that represents that of the selected population. developed based on a dimensional analysis approach to geometric scaling in which three scaling ratios Anthropometric variation between subjects such as containing the fundamental dimensions of mass, differences in height and weight can obviously affect length, and time must be defined in order to derive the magnitude of the response data, but differences in scaling ratios for other engineering variables of factors such as body mass distribution (i.e., fat-to- interest. Two of these ratios were defined to assume muscle ratio) can not only affect the magnitude but constant density and modulus of elasticity among also affect the phase or timing of the response data, subjects; the third ratio is the total body mass ratio: which is especially critical to the creation of a mean ρ E M response curve. Figure 1 shows an example of two 1 = 50th 1 = 50th λ = 50th (1) ρ curves (blue and red) which are out of phase but sub Esub M sub similar in shape and magnitude. The resulting mean curve (black) is bimodal, much lower in magnitude, where ρ is density, E is the modulus of elasticity, and has a shape nothing like either of the individual curves. Ideally, normalization would be able to M is total body mass, λ is the total body mass th account for the variation between the subjects which scaling ratio, and the subscripts “50 ” and “sub” caused this out-of-phase response, thus resulting in a represent the “standard” subject and test subject, more representative mean response curve. respectively. Note that since the most common th “standard” subject is the 50 percentile male it will th Although several methods for normalizing human hereafter be referred to with the subscript “50 ”, and subject test data can be found in the literature, the M 50th can be easily obtained from anthropometric two most commonly implemented procedures are tables. mass-based normalization as described by Eppinger (1984), and impulse momentum-based normalization Normalizing factors for engineering variables of as described for single mass systems (e.g., sled & interest (L = length or deflection, F = force, drop tests) by Mertz (1984) and for two-mass A = acceleration, T = time, and V = velocity) can then systems (e.g., pendulum tests) by Viano (1989). be derived from the three ratios in Equation (1) in conjunction with fundamental laws of physics, as Mass-based normalization shown in Equations (2) – (6): (Eppinger et al, 1984) M 1 The mass-based procedure normalizes human subject ρ = ⇒ L = λ 3 L (2) response data based solely on a mass ratio involving L3 50th sub the subject’s total body mass and the total body mass of the “standard” subject to which the responses are to be normalized. The underlying theory was
Moorhouse 2 F 2 and then models the impacts as a simple spring-mass E = ⇒ F = λ 3 F (3) system: L2 50th sub m k λ = 50th λ = 50th m k (7) −1 m k F = MA ⇒ A = λ 3 A (4) sub sub 50th sub For the mass ratio, instead of a simple ratio of total L 1 body mass, an effective mass of the impacted body A = ⇒ T = λ 3T (5) T 2 50th sub region is estimated from the response data using an impulse momentum analysis as shown in Equation L (8): = = T V ⇒ V50th Vsub (6) T Fdt T = = ∫0 Fdt meff v0 ⇒ meff (8) ∫0 v The strengths of mass-based normalization are that it 0 is easy to implement, the procedure is independent of test condition (i.e., the same procedure is used for where meff is the effective mass, F is the force sled tests, drop tests, and pendulum tests), and the adjustment made to the response data is directly during impact, vo is the change in velocity during linked to the easy-to-obtain anthropometry measure the impact, and T is the duration of impact. By of total body mass. The fact that the response data is incorporating the response data in the normalization adjusted based solely on total body mass may make it procedure, some of the other causes for variation easy to implement, but it could also be considered a besides anthropometry (discussed earlier) can be weakness because measures of anthropometry alone somewhat accounted for. Unlike the total body mass are often poor predictors of response data. The ratio where the mass of the 50th percentile male is physical variation in the subjects includes not just easily obtained from anthropometric tables, the anthropometry but also variables such as age, gender, standard effective mass of the 50th percentile male, nutrition, pathology, etc. which cannot be accounted m , is dependent on the test condition and is thus for and predicted by anthropometry. In addition, 50th adjusting the signals based solely on total body mass typically unknown. Therefore the value is estimated often does not work well for component-level tests by calculating the ratio of each subject’s effective such as pendulum impacts. mass to their total body mass, averaging the ratio across subjects, and multiplying by the total body mass of the population to which the data is to be A limitation of this type of normalization is that the th underlying theory for geometric scaling forces an normalized (e.g., 76 kg for a 50 percentile male). assumption of full-body geometric similitude (i.e., the ratio of lengths at one body region applies to all For the stiffness ratio, Mertz (1984) showed that by other body regions as well) even though in reality assuming a constant modulus among subjects and body regions are often proportioned differently from geometric similitude within the impacted body subject-to-subject. Also, while the two fundamental region, the stiffness ratio could be approximated material constituency assumptions of constant density using a ratio of characteristic lengths. For example, and constant modulus among subjects are likely if the impact involves the thorax then chest depth or reasonable approximations, there will of course be chest breadth might be chosen as the characteristic some variation. The biggest limitation to this method length used to calculate the stiffness ratio. Once a characteristic length is chosen, the corresponding is that the response data of a tall and thin osteoporotic th subject with the same total body mass as an length for a 50 percentile male can be obtained from overweight and short healthy-boned subject would anthropometric tables. scale identically, implying that they would be expected to exhibit a similar response to an identical Normalizing factors for engineering variables of impact. interest (t = time, a = acceleration, v = velocity, x = length or deflection, and F = force) can then be Impulse momentum-based normalization derived from the mass ratio and stiffness ratio in (Mertz, 1984; Viano, 1989) Equation (7) in conjunction with the solution to the differential equations of motion for a simple spring- This procedure normalizes human subject response mass system, as shown in Equations (9) – (13): data based on both a mass ratio and a stiffness ratio,
Moorhouse 3 m λ t = π ⇒ t = m t (9) ()+ 50th λ sub m p msub k k F = λ λ F (18) 50th m k ()+ sub m p m50th k ⎛ k ⎞ a = − v sin ⎜ t ⎟ The primary strength of this normalization method is o ⎜ ⎟ m ⎝ m ⎠ that it incorporates the response data so that it can λ potentially account for variation in response arising ⇒ a = k a (10) from subject differences other than just 50th λ sub m anthropometry. A weakness with this procedure involves using a characteristic length for the stiffness ratio, because the choice of which characteristic length to use is somewhat subjective. Also, using a ⎛ k ⎞ characteristic length as a surrogate for stiffness v = − v cos ⎜ t ⎟ ⇒ v = v (11) o ⎜ m ⎟ 50th sub requires the assumptions of constant modulus and ⎝ ⎠ geometric similitude within the impacted body region. However, if the effective stiffness of the subject could be estimated from the response data, m ⎛ k ⎞ similar to the effective mass, then those assumptions x = v sin ⎜ t ⎟ o ⎜ ⎟ would not be necessary. k ⎝ m ⎠ λ To date, there is no quantitative consensus as to ⇒ x = m x (12) which of the normalization techniques discussed 50th λ sub k above is most effective. Furthermore, some areas of potential improvement for both methods have been ⎛ k ⎞ F = − v km sin ⎜ t ⎟ identified. Therefore, the goal of this study was to o ⎜ m ⎟ quantify the effectiveness of the two existing ⎝ ⎠ normalization procedures as well as some new = λ λ ⇒ F50th m k Fsub (13) methodologies developed in this study based on the identified potential improvements. Note that the normalizing factors shown in Equations (9) - (13) were derived from the equation for a single METHODS mass, single spring system so they are only valid for sled tests and drop tests where the impacting mass Potential improvements to existing can be assumed infinite. For pendulum impacts, the normalization methods equations of motion for a two-mass system are used After reviewing the two most common existing to derive the normalizing factors shown in Equations normalization methods, some weaknesses and (14) – (18), where mp is the mass of the impactor. potential areas of improvement were identified, and some new methodologies were developed to address ()+ these areas. For the mass-based normalization the λ m p msub t = m t (14) most prominent limitation is that body mass 50th λ ()+ sub distribution is unaccounted for. Therefore, replacing k m p m50th the ratio of total body mass with a ratio involving a
measure of “body type” such as the Body Mass Index ()+ λ m p msub (BMI) in Equation (19), or the Ponderal Index (PI) in a = k a (15) 50th λ ()+ sub Equation (20), was investigated as a potential m m p m50th improvement. Mass BMI = (19) = 2 v50th vsub (16) Height
()+ 3 λ m p msub ⎛ Mass ⎞ x = m x (17) PI = 10 ⎜ ⎟ (20) 50th λ ()+ sub ⎜ ⎟ k m p m50th ⎝ Height ⎠
Moorhouse 4 For the impulse momentum-based normalization it Full-body side impact sled test data set would be valuable to know the importance of the (Maltese et al., 2002) choice of characteristic length in the stiffness ratio, so various characteristic lengths and combinations of For the sled test data set, normalization procedures characteristic lengths (i.e., aspect ratios) were were evaluated for all test conditions that contained evaluated. Specifically, a characteristic length was three or more subjects after a subject exclusion measured along each of the three axes of the body evaluation. Subjects were excluded if they failed a coordinate system (e.g., chest depth, chest breadth, conservation of momentum check (Nusholtz et al., and chest height), directly along the line of impact, 2007) or if there was significant “leaning” which was and around the circumference of the impacted area. defined as the pelvis contacting the flat wall more Each of these measurements was then used as the than 10 ms after the thorax (Irwin et al., 2005). Four characteristic length for the stiffness ratio as well as test conditions with three or more subjects remained multiple combinations of each of these for the evaluation after subject exclusion: Rigid measurements. High-Speed Flat Wall (RHF), Padded High-Speed Flat Wall (PHF), Rigid Low-Speed Flat Wall (RLF), Also, replacing the characteristic length estimate of and Padded Low-Speed Flat Wall (PLF). stiffness with an actual estimate of the effective stiffness calculated from the response data was The thoracic deflection for each subject was obtained investigated as a potential improvement. As long as by averaging the half-deflections measured by the deflection data for the relevant body region is upper and middle thoracic chestband signals (if they measured, a methodology somewhat analogous to both existed), or using the half-deflection from either Equation (8) for calculating an effective mass can be the upper or the middle thoracic chestband signals (if implemented to estimate an effective stiffness, as only one existed). Although Maltese (2002) illustrated in Equation (21): calculated both full- and half-deflections, half- deflections were utilized in this study as they were 1 deemed more relevant for comparison with an ATD. Fdx = k x2 ∫ eff max 2 The normalization techniques were applied to several 2 Fdx signal groups from the four sled test conditions = ∫ including multiple time-histories (Thorax Loadwall, ⇒ keff 2 (21) xmax Abdomen Loadwall, Pelvis Loadwall, Upper Spine Y accel, Lower Spine Y accel, Pelvis Y accel, Thoracic where keff is the effective stiffness, F is the force Deflection) as well as the force-deflection responses for the thorax (F-D Thorax). during impact, and xmax is the maximum displacement during the impact. As with the effective mass in the impulse momentum-based normalization, Lateral and oblique pendulum side impact data set the standard effective stiffness of the 50th percentile (Shaw et al., 2006) male, k50th , is dependent on the test condition and is For the pendulum impact data set, normalization thus unknown. Therefore the value is estimated by procedures were evaluated for both the lateral impact calculating the ratio of each subject’s effective test condition and the oblique impact test condition, stiffness to a characteristic length of the subject (e.g., and no subjects were excluded based on the criteria chest breadth for a thoracic side impact), averaging discussed above. the ratio across subjects, and multiplying by the characteristic length of the population to which the Shaw (2006) only reported results for full-deflection data is to be normalized. of the thorax, but half-deflections were also calculated in the study and the corresponding Data sets for normalization evaluation electronic data was obtained via personal communication and used for this evaluation to be Two data sets were chosen for the normalization consistent with the full-body sled test data set. evaluation – a full-body side impact sled test data set (Maltese et al., 2002) and a component-level thorax The signal groups analyzed for both the lateral and pendulum impact data set (Shaw et al., 2006). oblique test conditions included the force-time histories (Force), deflection-time histories (Deflection), and force-deflection responses (F-D).
Moorhouse 5 Assessment of efficacy of normalization was then calculated (analogous to a standard techniques deviation), and divided by the product of the force and deflection value at each point (analogous to a Each normalization technique was evaluated based mean value), thus producing a measure for force- on its ability to collapse each group of curves to map deflection responses (%CVellipse) which is analogous onto a single response, because ideal normalization to the %CV for time histories. The %CVellipse value should not only adjust the response data to the at each point was averaged across the time period appropriate target population but also remove which included the intersection of the upper 80% of subject-to-subject variation due to differences in the mean force magnitude and the upper 80% of the anthropometry and physical characteristics (e.g., age, mean deflection magnitude. As with %CV, lower gender, nutrition, pathology, etc.). Therefore a values of %CVellipse represent better grouping of the quantifiable assessment of the similitude of a group force-deflection curves, and hence more effective of curves was required. normalization.
Time histories RESULTS
Since the percent coefficient of variation (%CV) is Although over thirty different variations of often used to assess the repeatability of a set of normalization techniques were evaluated, the similar ATD responses, this quantity was deemed majority of these variations involved different appropriate to assess the efficacy of the normalization choices of characteristic length used to calculate the techniques for the time-histories: stiffness ratio in the impulse momentum-based σ procedure (see Methods section). However, no %CV = ×100 (22) μ discernible difference in the effectiveness of the impulse-momentum normalization procedure could where be identified based on the choice of characteristic length, so the results for each individual choice of σ is the standard deviation of the responses characteristic length will not be shown. Also for the μ is the mean of the responses mass-based normalization, utilizing a ratio of BMI and/or PI instead of the total body mass ratio did not Although this measure is typically calculated for yield a noticeable difference in normalization single value peak responses, in this study it was effectiveness, so these methodologies will also not be important to evaluate the similitude of the curves presented. across time as well. Therefore the %CV was The results from three normalization procedures will calculated at each point in time and then averaged to be presented in detail in this manuscript along with produce an average %CV across time. Also since the the non-normalized data for reference (referred to as %CV metric does not perform well at low “Non-normalized”). The first methodology, referred magnitudes of the response (i.e., when the mean to as “Mass-based”, is the existing mass-based value approaches zero), the %CV was only calculated normalization procedure using a ratio of total body for the time period which included the upper 80% of mass. The second methodology, referred to as “Eff the mean response (i.e., for values of the mean Mass & Char Length”, is the standard impulse response that are greater than 20% of the peak momentum-based procedure using a ratio of effective magnitude of the mean curve). This average %CV mass for the mass ratio and a ratio of characteristic value provides a relative measure of how similar the lengths for the stiffness ratio. The characteristic curves are, where a lower average %CV indicates lengths were chosen in this evaluation to be better grouping of the curves. consistent with previous studies where the respective data sets were normalized using the impulse Force-deflection histories momentum-based method. Therefore, chest depth was used for the sled test data (Irwin, 2005) and chest To evaluate the similitude of a group of force- breadth for the pendulum impact data (Shaw, 2006). deflection curves, an analogous %CV value for force- The third methodology, referred to as “Eff Mass & deflection space was generated. First, an ellipse was Eff Stiff”, utilizes a ratio of effective mass for the formed about each point of the mean force-deflection mass ratio and a ratio of effective stiffness calculated response with semi-major and semi-minor axes of from the response data as in Equation (21) for the length equal to one standard deviation each in force stiffness ratio. and deflection (Shaw, 2006). The area contained within each of these one standard deviation ellipses
Moorhouse 6 The results from the normalization evaluation are together, resulting in a 60.9% improvement in the given in Table 1 for the full-body side impact sled %CV value. The trend revealed above indicates that test data set and in Table 2 for the component-level incorporating the response data into the thorax pendulum impact data set. Since the average normalization process results in better grouping of %CV and %CVellipse were both utilized as relative curves and thus more effective normalization. measures of the effectiveness of a given normalization procedure, the percent improvement over the “Non-normalized” data are reported in "Non-normalized" RHF Thorax Loadwall Tables 1 and 2 for each of the three normalization 18000 techniques, rather than the actual numeric values of 16000 the measures. The normalization method resulting in 14000 the largest percent improvement for each signal 12000 group is highlighted in green. 10000 %CV=%CV 64.7 = 60.2% For the full-body sled tests, Table 1 shows that for 8000 the eight signal groups that were analyzed in each of (N) Force the four test conditions (RHF, PHF, RLF, and PLF), 6000 the “Eff Mass & Eff Stiff” normalization approach 4000 performed the best (i.e., resulted in the largest 2000 amount of improvement in curve grouping) for six of 0 the eight RHF and RLF signal groups, seven of the -10 0 10 20 30 40 50 60 70 80 Ti me (ms) eight PHF signal groups, and five of the eight PLF signal groups. For the component-level pendulum impacts, Table 2 shows that for the three signal Figure 2. “Non-normalized” RHF thorax loadwall groups that were analyzed in each of the two test time-histories (%CV = 64.7) conditions (Lateral and Oblique), the “Eff Mass & "Mass-based" RHF Thorax Loadwall Eff Stiff” normalization approach performed the best 18000 in five of the six signal groups. In full, the “Eff Mass & Eff Stiff” normalization approach performed the 16000 best in 29 of 38 (~76%) of the signal groups 14000 analyzed, as compared to 7 of 38 (~18%) for the 12000 “Mass-based” approach and 2 of 38 (~5%) for the 10000 “Eff Mass & Char Length” approach. %CV=%CV 45.1= 43.1% 8000
(N) Force DISCUSSION 6000
4000 Normalization of time histories 2000 To illustrate an example of normalization on time- 0 histories, the thorax loadwall time-histories for the -10 0 10 20 30 40 50 60 70 80 Ti me (ms) RHF condition are shown for the “Non-normalized” condition in Figure 2, and the “Mass-based”, “Eff Mass & Char Length”, and “Eff Mass & Eff Stiff” Figure 3. “Mass-based” RHF thorax loadwall time- normalization conditions in Figure 3-5, respectively. histories (%CV = 45.1) Visual inspection of Figures 2 and 3 reveals that “Mass-based” normalization results in a small level of improvement in curve group similitude, and in fact the average %CV improves from 64.7 to 45.1 for a percent improvement of 30.3%. Inspection of Figures 2 and 4 shows that the “Eff Mass & Char Length” normalization results in an even more significant improvement in the curve grouping, with a corresponding 42.8% improvement in the %CV value. Finally, inspection of Figures 2 and 5 illustrates that the “Eff Mass & Eff Stiffness” normalization is very effective at bringing the curves
Moorhouse 7 "Eff Mass & Char Length" RHF Thorax Loadwall "Non-normalized" F-D Oblique Thorax Pendulum Impacts 18000 1800
16000 1600 %CVCumulativeellipse Ellipse = 19.8% Error = 5.02 14000 1400
12000 1200
10000 1000 %CV=%CV 37.0 = 30.1% 8000 800 Force (N) Force (N) Force
6000 600
4000 400
2000 200
0 0
-10 0 10 20 30 40 50 60 70 80 0 10 20 30 40 50 60 70 80 Ti me (ms) Deflection (mm)
Figure 4. “Eff Mass & Char Length” RHF thorax Figure 6. “Non-normalized” Oblique thorax force- loadwall time-histories (%CV = 37.0) deflection histories (%CVellipse = 19.8%)
"Eff Mass & Eff Stiff" RHF Thorax Loadwall "Mass-based" F-D Oblique Thorax Pendulum Impacts 18000 1800
16000 1600 %CVCumulativeellipse Ellipse = 24.0% Error = 6.00 14000 1400
12000 1200
10000 1000 %CV=%CV 25.3 = 19.1% 8000 800 Force (N) Force Force (N) Force
6000 600
4000 400
2000 200
0 0
-10 0 10 20 30 40 50 60 70 80 0 10 20 30 40 50 60 70 80 Ti me (ms) Deflection (mm)
Figure 5. “Eff Mass & Eff Stiff” RHF thorax loadwall Figure 7. “Mass-based” Oblique thorax force- time-histories (%CV = 25.3) deflection histories (%CVellipse = 24.0%)
Normalization of force-deflection histories "Eff Mass & Char Length" F-D Oblique Thorax Pendulum Impacts 1800 To illustrate an example of normalization on force- 1600 Cumulative%CVellipse Ellipse = Error18.5% = 4.59 deflection histories, the force-deflection curves for 1400 the oblique thorax pendulum impacts are shown for the “Non-normalized” condition in Figure 6 and the 1200 “Mass-based”, “Eff Mass & Char Length”, and “Eff 1000
Mass & Eff Stiff” normalization conditions in 800 Figures 7-9, respectively. The grey shaded regions (N) Force 600 represent the one standard deviation ellipses defined in the Methods section and in Shaw (2006). Note 400 that low values of the %CVellipse value represent 200 better grouping of the curves and typically 0 correspond to noticeably smaller regions of grey 0 10 20 30 40 50 60 70 80 shading. Deflection (mm) Figure 8. “Eff Mass & Char Length” Oblique thorax force-deflection histories (%CVellipse = 18.5%)
Moorhouse 8 "Eff Mass & Eff Stiff" F-D Oblique Thorax Pendulum Impacts methodology performed the best. It is likely that the 1800 complexity of these signals, and the additional 1600 %CVCumulativeellipse Ellipse = 7.6%Error = 1.91 potential sources for variation associated with the 1400 installation of the instrumentation, greatly reduce the effectiveness of normalization for these “internal” 1200 signals. However, if the analysis of the results is 1000 limited to the other 26 signal groups (i.e., force-time, 800 deflection-time, and force-deflection), normalization Force (N) Force
600 is much more effective in improving the grouping of the curves, and the “Eff Mass & Eff Stiffness” 400 approach clearly performs the best. Specifically, it 200 yields the greatest improvement in 21 of 26 (~81%)
0 of these signal groups, as compared to 4 of 26
0 10 20 30 40 50 60 70 80 (~15%) for the “Mass-based” approach and 1 of 26 Deflection (mm) (~4%) for the “Eff Mass & Char Length” approach.
Figure 9. “Eff Mass & Eff Stiff” Oblique thorax force- Limitations deflection histories (%CV = 7.6%) ellipse Although the results from this study demonstrate that Close visual inspection of Figures 6 and 7 reveals the normalization of impact response data using the that the grey shaded error region actually gets a little “Eff Mass & Eff Stiff” approach is the most effective bigger with “Mass-based” normalization, and in fact way of those examined to improve the similitude of a group of responses for the creation of a mean human the average %CVellipse increases from 19.8 to 24.0 resulting in a negative percent improvement of response curve, some limitations in the methodology -21.2%. As mentioned earlier, normalization based should be pointed out. First, the values for effective solely on total body mass often does not perform well stiffness can only be obtained if deflection data is in component-level tests like pendulum impacts. measured directly (e.g., chestband) or can be Inspection of Figures 6 and 8 shows that the “Eff indirectly estimated (e.g., double integration of Mass & Char Length” normalization results in a accelerometers). Also, the numerator of the stiffness modest reduction in the grey shaded error region, ration in Equation (7) for “Eff Mass & Eff Stiff” with a corresponding 6.6% improvement in the normalization is dependent on the test condition and cannot be obtained from anthropometric tables. %CVellipse value. Finally, inspection of Figures 6 and 9 reveals that the “Eff Mass & Eff Stiffness” Recall that this is also true for the numerator of the normalization causes a rather dramatic alignment of effective mass ratio. However, the effective mass and effective stiffness can still be estimated and the curves and large improvement in the %CVellipse th value of 61.6%. related directly back to the 50 percentile male (or selected population), using standard anthropometric Additional Discussion values as discussed previously.
Several additional observations can be made from SUMMARY examination of Tables 1 and 2. For the component- level pendulum impacts, the “Mass-based” Several normalization methodologies were normalization approach actually caused the grouping quantitatively evaluated by applying them to time- of the curves to get worse than the “Non-normalized” history data and force-deflection data from both a data in all six signal groups, as evidenced by the full-body sled test data set and a component-level negative percent improvements. This again supports pendulum impact data set. The normalization the indication that total body mass normalization technique (of those examined) found to consistently does not perform well in component-level tests. perform the best is a newly developed extension of impulse-momentum-based normalization in which For the upper spine, lower spine, and pelvis the stiffness ratio was determined from effective acceleration signals in the sled test data set, there stiffness values calculated from the test data, rather were many instances where one or all of the than using characteristic lengths. Utilization of this normalization techniques did not improve the curve normalization methodology in the development of grouping relative to the non-normalized data. mean human response curves may prove useful in Furthermore, if the analysis of the normalization more accurately characterizing the target human results is limited to only these 12 acceleration signal response to aid in the design of more biofidelic groups, it is much less clear which normalization dummies.
Moorhouse 9 Table 1. Normalization results for the full-body side impact sled test data set
Mass-Based Eff Mass & Char Length Eff Mass & Eff Stiff Signal (% improvement) (% improvement) (% improvement) Thorax Loadwall 30.3 % 42.8 % 60.9 % Abdomen Loadwall 13.1 % 25.9 % 28.1 % Pelvis Loadwall 12.7 % 5.8 % 41.2 % Upper Spine Y accel 13.8 % 5.1 % 18.9 % RHF Lower Spine Y accel 11.1 % -23.2 % 10.2 % Pelvis Y accel -2.1 % -6.4 % 14.0 % Thoracic Deflection 13.2 % -60.6 % -21.2 % F-D Thorax 40.6 % 9.5 % 70.7 % Thorax Loadwall 40.3% 42.2 % 57.0 % Abdomen Loadwall 3.6% 35.1 % 54.8 % Pelvis Loadwall 55.0% 48.3 % 67.7 % Upper Spine Y accel 5.4% 8.1 % 7.6 % PHF Lower Spine Y accel 9.4% 13.9 % 17.1 % Pelvis Y accel 7.6% 8.8 % 9.4 % Thoracic Deflection 36.3% 22.4 % 40.3 % F-D Thorax 60.3 % 56.2 % 70.1 % Thorax Loadwall 9.5 % 19.8 % 23.4 % Abdomen Loadwall 3.0 % 30.3 % 36.0 % Pelvis Loadwall 2.1 % 10.1 % 27.6 % Upper Spine Y accel -8.7 % -54.7 % -25.4 % RLF Lower Spine Y accel -0.7 % -2.8 % 0.2 % Pelvis Y accel 5.6 % 2.9 % 0.6 % Thoracic Deflection -17.4 % -51.9 % -4.4 % F-D Thorax -1.3% -5.7 % 24.1 % Thorax Loadwall 40.4 % 5.6 % 18.2 % Abdomen Loadwall 28.1 % 43.8 % 46.7 % Pelvis Loadwall 3.7 % -37.7 % 30.8 % Upper Spine Y accel -8.6 % -8.6 % -7.9 % PLF Lower Spine Y accel 6.6 % 7.0 % 8.4 % Pelvis Y accel 16.3 % -25.8 % 25.8 % Thoracic Deflection 28.7 % 21.4 % 26.9 % F-D Thorax 55.1 % 0.9 % 20.3 %
Table 2. Normalization results for the component-level thorax pendulum impact data set
Mass-Based Eff Mass & Char Length Eff Mass & Eff Stiff Signal (% improvement) (% improvement) (% improvement) Force -16.5 % 9.0 % -20.3 % Lateral Deflection -2.8 % 14.4 % 25.5 % F-D -25.0 % 21.0 % 25.0 % Force -7.8 % 5.9 % 34.8 % Oblique Deflection -14.0 % 5.4 % 41.0 % F-D -21.2 % 6.6 % 61.6 %
Moorhouse 10 REFERENCES SHAW, J. M., HERRIOT, R. G., MCFADDEN, J. D., DONNELLY, B. R., and J. H BOLTE, IV CAVANAUGH, J. M., NYQUIST, G. W., T., (2006). Oblique and Lateral Impact Response of GOLDBERG, S. J., and KING, A. I. (1986). the PMHS Thorax. Proc. 50th Stapp Car Crash Lower abdominal tolerance and response. Proc. Conference, pp 147-167. 30th Stapp Car Crash Conference, pp. 41-63. VIANO, D. C., (1989). Biomechanical responses and EPPINGER, R. H., MARCUS, J. H., and MORGAN, injuries in blunt lateral impact. SAE 892432. R. M. (1989). Development of dummy and injury Society of Automotive Engineers, Warrendale, index for NHTSA’s thoracic side impact PA. protection research program. SAE 840885. Society of Automotive Engineers, Warrendale, PA. IRWIN, A. L., SUTTERFIELD, A., HSU, T. P., MERTZ, H. J., ROUHANA, S. W., and SCHERER, R. (2005). Side impact response corridors for the rigid flat-wall and offset-wall side impact tests of NHTSA using the ISO method of corridor development. Proc. 49th Stapp Car Crash Conference, pp 423-456. ISO/TR9790. (1999). Road vehicles-lateral impact response requirements to assess the biofidelity of the dummy. Technical Report No. 9790, International Standards Organization, American National Standards Institute, New York, NY. LOBDELL, T.E., KROELL, C. K., SCHNEIDER, D. C., and HERING, W. E. (1973). Impact response of the human thorax. Proc. Symposium on Human Impact Response, Plenum Press, New York, NY, pp. 201-245. MALTESE, M. R., EPPINGER, R. H., RHULE, H. H, DONNELLY, B. R., PINTAR, F. A., and YOGANANDAN, N. (2002). Response corridors of human surrogates in lateral impacts. Proc. 46th Stapp Car Crash Conference, SAE 2002-22-0017, pp 321-351. MERTZ, H. J., (1984). A procedure for normalizing impact response data. SAE 840884. Society of Automotive Engineers, Warrendale, PA. MORGAN, R. M., MARCUS, J. H., T., and EPPINGER, R. H. (1986). Side impact – the biofidelity of NHTSA’s proposed ATD and efficacy of TTI. Proc. 30th Stapp Car Crash Conference, pp. 27-40. NUSHOLTZ, G. S., HSU, T. P., BYERS, L. C. (2007). A proposed side impact ATD bio-fidelity evaluation scheme using cross-correlation approach. Proc. 20th International Technical Conference on the Enhanced Safety of Vehicles (ESV), Paper Number 07-0399.
Moorhouse 11