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Report
Detailed Seismic Assessment – Sir Howard Morrison Performing Arts Centre
Prepared for Rotorua Lakes Council (Client)
Prepared by Beca Limited (Beca)
23 April 2018
Detailed Seismic Assessment – Sir Howard Morrison Performing Arts Centre
Beca // 23 April 2018
5640377 // NZ1-14797867-23 0.23 // ii
Executive Summary
Background
Beca has been engaged to prepare a Detailed Seismic Assessment (DSA) report for Rotorua Lakes Council
(RLC), the owner of the Sir Howard Morrison Performing Arts Centre (SHMPAC) located at 1170 Fenton
Street, Rotorua, to describe the results of our quantitative assessment. This assessment follows a Seismic
Assessment Review for the building dated 28 April 2015 which included a high level independent structural
assessment of the seismic capacity of the building. Beca has also previously completed a Concept Seismic
Strengthening Report Targeting 67%NBS, dated 23 January 2017 based on the previous high level seismic
assessment.
Building Description
The Sir Howard Morrison Performing Arts Centre was constructed circa 1938 for the Rotorua Borough
Council. The building is comprised of multiple structures at different elevations, predominantly without any
seismic separations with the exception of the Boiler/Transformer Room, and Stairwell at the western end of
the Concert Hall. The different areas of the building are labelled in Figure 1.
Since construction, the building has undergone a number of extensions, alterations and refits including some
limited earthquake strengthening. However, a large portion of the structure remains unchanged.
The building is listed by Heritage New Zealand as a ‘Historic Place Category 1’ structure.
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Figure 1: Locations of Structures that Make Up the Building
Assessed Seismic Rating
The results of our quantitative seismic assessment indicate the building’s earthquake rating is currently less
than 34%NBS (New Building Standard) assessed in accordance with the guideline document The Seismic
Assessment of Existing Buildings - Technical Guidelines for Engineering Assessments, dated July 2017.The
focus of the assessment using these guidelines is on the life safety of those occupying and those
immediately outside the building, rather than building damage and reparability considerations or business
interruption.
The earthquake rating is based on an Importance Level 3 (IL3) structure, with the exception of the external
stairwell adjacent to the Concert Hall, Transformer and Boiler House which are importance Level 2 (IL2)
structures. For all structures a design life of 50 years has been adopted, in accordance with the joint
Australian/New Zealand Standard – Structural Design Actions Part 0, AS/NZS 1170/0:2002, as being
deemed appropriate for this building.
This site subsoil class for this DSA has been based on class D for assessment of the primary structural
system and class C when considering parts loading in accordance with the New Zealand Design Standard –
Structural design actions Part 5: Earthquake actions, NZS 1170.5:2004. The reason for this is conflicting
results from previous geotechnical reporting of the site subsoil class. In terms of earthquake loading we have
adopted the more onerous soil class.
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Our assessment concludes that the building is currently a Grade D building following the Engineering
Assessment Guidelines building grading scheme. Grade D buildings represent a life-safety risk to occupants
comparable to 10-25 times that expected for a new building, indicating a high risk exposure.
A building with an earthquake rating less than 34%NBS fulfils one of the requirements for the Territorial
Authority to consider it to be an Earthquake-Prone Building (EPB) in terms of the Building Act 2004. A
building rating less than 67%NBS is considered as an Earthquake Risk Building (ERB) by the New Zealand
Society for Earthquake Engineering. Since the Sir Howard Morrison Performing Arts Centre is currently less
than 34%NBS it is possible Rotorua Lakes Council may determine the buildings status as earthquake prone.
Our assessment identified the following structural weaknesses or items scoring <67%NBS, in the building:
Table 1: Summary of seismic scores for areas <67%NBS
System Direction %NBS Failure
type
Notes
Foyer Truss Transverse (N-S
direction)
25%NBS Ductile Buckling of the bottom chord. Sensitive to
soil-structure interaction effects and
interaction between the north and south
wings.
Supper
Room/Kitchenette
walls
Both directions
25%NBS Brittle Unreinforced concrete block wall out of plane, and a suspended unreinforced pumice concrete block wall with no reliable load path.
Storage Room Transverse (N-S)
directions
25%NBS Ductile
/Brittle
Reinforced concrete wall out-of-plane and
potential loss of gravity support to plant
support beams.
North Wing Frame Transverse (N-S)
directions
45%NBS Brittle Governed by the beam – column joint
detailing. Assuming no diaphragm or other
mitigating measures.
Northeast Wing
Frame
Transverse (N-S)
direction
50%NBS Brittle Our calculations determined that ‘failure’ of
the roof truss, could occur at <34%NBS,
resulting in redistributed and alternate load
paths/ mechanisms being activated to
maintain roof support. The steel roof truss
fixings in combination with a lack of robust
diaphragm or roof bracing system, appear
to be particularly deficient.
Concert Hall
Frame
Transverse (N-S)
direction
30%NBS Ductile Buckling of the props. This is the result of
changing from Soil Class C to Soil Class D,
after prop design, based on further
geotechnical data being made available.
North/South Wing
end walls
Longitudinal (E-W )
direction
30%NBS Brittle Unreinforced pumice concrete block wall.
Invasive investigations suggest the outer
whythes are unsupported out of plane.
Supper Room
Walls
Longitudinal (E-W)
and Transverse (N-
S) directions
45%NBS Brittle Unreinforced pumice concrete block walls
out of plane.
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System Direction %NBS Failure
type
Notes
North Wing Admin
Walls
Transverse (N-S)
directions
55%NBS Brittle Unreinforced pumice concrete block walls
out of plane.
Currently the walls have a Polyplast layer
for out of plane strength, however we don’t
consider this provides any substantial
increase in capacity.
Auditorium Transverse (N-S)
directions
50%NBS Ductile Frame governed by ultimate drift limits, due
to loss of frame action from roof truss end
diagonal member buckling.
Fly Tower Both directions 25%NBS Brittle Deficient Reid brace connectors at ends of
cross bracing, typical.
Transverse 32%NBS Brittle Potential for loss of gravity support to truss
over proscenium arch.
Dressing Room Both directions 45%NBS Brittle The diaphragm capacity is limited by the
collector and tie capacities.
Function Room Both directions >90%NBS Ductile Our calculations determined that the roof
beams were the critical elements in the
frame and could resist levels of earthquake
shaking to at least 90% ULS (IL3).
The low %NBS is compounded by the fact that some of the failures are characterised as ‘brittle’, as noted in
the table above. A brittle failure mode is essentially an instantaneous failure with little or no warning.
Essentially load builds up in an element before snapping and, once this happens, the element has no further
capacity to distribute load.
A ‘ductile’ failure is a more favourable failure as the section can undergo some deformations and maintain
vertical support without collapse. Essentially the member/connection will bend and stretch without snapping.
As such, the building can dissipate or absorb seismic forces by deforming and still support the weight of the
building and resist some lateral load. Generally, ductile systems, although potentially significantly damaged
post-earthquake pose a reduced life-safety risk.
There have been significant advances in seismic loading and design principles since this building was initially
designed. It is therefore expected that the older structures of this building are not up to current building
standards and the findings of this report are consistent with the buildings age.
Previous Assessment
The previous high level Seismic Assessment was undertaken in accordance with the New Zealand Society
for Earthquake Engineering (NZSEE) guidelines for Assessment and improvement of the Structural
Detailed Seismic Assessment – Sir Howard Morrison Performing Arts Centre
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Performance of Buildings in earthquakes1. The high level assessment focussed on the higher risk older
structures that were constructed between the 1930s and 1971 as follows;
� Concert Hall. � Supper Room. � North-West Wing. � North-East Wing. � Auditorium.
This Detailed Seismic Assessment considers all structures that make up SHMPAC including the more
modern sections of the building that were not considered in the previous assessment.
Next Steps We recommend you consider carrying out the following steps:
� Review the seismic strengthening schemes and associated cost estimate in the separate cost report.
� Consult with the Heritage Architect in relation to the strengthening proposed.
� Coordinate any other upgrade works proposed to the building.
� Undertake detailed design of the strengthening schemes
1 NOTE: The New Zealand Society for Earthquake Engineering (NZSEE) guidelines for Assessment and
improvement of the Structural Performance of Buildings in earthquakes was replaced by The Seismic
Assessment of Existing Buildings - Technical Guidelines for Engineering Assessments, for seismic
assessments in New Zealand in July 2017.
Detailed Seismic Assessment – Sir Howard Morrison Performing Arts Centre
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Contents
1 Introduction ........................................................................................................ 3
Scope of Assessment ...................................................................................................................... 3
Previous Assessment ...................................................................................................................... 3
Regulatory Environment and Design Standards ............................................................................. 4
Assessment Methodology................................................................................................................ 5
Explanatory Statement .................................................................................................................... 5
2 Building Description .......................................................................................... 7
General ............................................................................................................................................ 7
Heritage status ................................................................................................................................. 8
Geotechnical Considerations ........................................................................................................... 9
Building Design .............................................................................................................................. 12
Structural Systems ......................................................................................................................... 13
3 Results of Seismic Assessment .................................................................... 16
Primary Seismic System Limiting Mechanisms ............................................................................. 18
Staircase and Safe Egress ............................................................................................................ 27
4 Commentary on Associated Seismic Risks .................................................. 30
Risks from Adjacent Buildings ....................................................................................................... 30
Risks from Non-structural Building Elements ................................................................................ 30
5 Assessment of Seismic Risk .......................................................................... 30
Seismic Risk and Performance Levels .......................................................................................... 30
6 Next Steps ........................................................................................................ 32
Appendices
Appendix A
Sources of Information
Appendix B
Concrete Test Report
Appendix C
Basis of Seismic Assessment
Appendix D
Building Inspection Photographs
Appendix E
Structural Drawings
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Detailed Seismic Assessment – Sir Howard Morrison Performing Arts Centre
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1 Introduction
Beca Ltd (Beca) has been engaged by Rotorua Lakes Council (RLC) to undertake a detailed seismic
assessment of the Sir Howard Morrison Performing Arts Centre (SHMPAC) located at 1170 Fenton Street,
Rotorua. This report describes the results of our quantitative seismic assessment. It follows on from the Seismic
Assessment Review Report dated 28 April 2015 and the Concept Seismic Strengthening Targeting 67%NBS
Report dated 23 January 2017.
Scope of Assessment
The purpose of this assessment is to establish the seismic risk and vulnerability of the Sir Howard Morrison
Performing Arts Centre. The assessment has been completed in accordance with the guidance documents The
Seismic Assessment of Existing Buildings – Technical Guidelines for Engineering Assessments, dated July
2017 (Engineering Assessment Guidelines) with the focus of life-safety of those occupying and those
immediately outside the building, rather than building damage and reparability considerations or business
interruption.
Our scope of work includes:
� A review of our previous high level Seismic Assessment and Concept Seismic Strengthening Targeting
67%NBS (IL3) reports.
� Review of the Council property files, structural drawings, geotechnical reports, intrusive and non-intrusive
on-site investigation findings, and photos from site.
� The assembly of an analytical model of the building structure based on the information gained by a review of
the drawings along with our site investigation and knowledge of the detailing used for structures of this era.
� An evaluation of the capacity of the key structural elements of the building and the seismic demands
(internal forces and ductility) on these elements, as derived from our analytical models.
� A brief commentary on the seismic hierarchy and attributes of key building features such as stairs, exterior
cladding, and the associated seismic risk.
� Preparation of concept level options for structural strengthening with order of magnitude costs.
� A summary of the findings and comments on any differences with the previous Seismic Assessment Review
and Concept Seismic Strengthening reports, and general recommendations about further actions.
Previous Assessment
Beca has previously completed an independent high level structural assessment of the seismic capacity of the
building which is summarised in our report dated 28 April 2015. The building was assessed on the basis of it
being an Importance Level 3 (IL3) structure, and a site subsoil class C, under the NZSEE Assessment and
Improvement of the Structural performance of Buildings in Earthquakes guidelines (current at the time of the
high level structural assessment)2. The high level assessment determined that the building has a rating of 35%
of the New Building Standard (%NBS) which corresponds to a Grade C building, indicating moderate risk as
defined by the NZSEE building grading scheme.
The high level structural assessment of the seismic capacity of the building provided a useful indication of the
building’s seismic rating in an earthquake, however the scope was limited to what was considered the higher
risk older structures constructed between the 1930s and 1971, Specifically;
� Concert Hall. � Supper Room.
2 NOTE: As of July 2017 the NZSEE Seismic Assessment guidelines were replaced by The Seismic
Assessment of Existing Buildings - Technical Guidelines for Engineering Assessments, dated July 2017.
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� North-West Wing. � North-East Wing. � Auditorium.
In this DSA the results from the previous assessment have been revised using a more comprehensive seismic
assessment, in accordance with the Engineering Assessment Guidelines. We have developed a 3D model of
the building in ETABS to aid us in assessing the interaction between different structures within the building. This
DSA assesses all areas of the building including the more modern structures which were not assessed
previously.
Regulatory Environment and Design Standards
The Earthquake-Prone Building regulatory framework underwent significant changes during 2016 and 2017 as
a result of learnings from the Christchurch earthquakes, and more recently, the 2016 Kaikoura earthquake. This
resulted in the Building (Earthquake-prone Buildings) Amendment Act 2016, the Building (Specified Systems,
Change the Use, and Earthquake-prone Buildings) Regulations 2017 including the Earthquake-prone Building
Methodology, and the technical guideline document The Seismic Assessment of Existing Buildings - Technical
Guidelines for Engineering Assessments. The important aspects of this regulatory framework are summarised
below.
Earthquake-Prone Buildings (EPBs) are defined in Section 133AB of the Building (Earthquake-prone Buildings)
Amendment Act 2016 as buildings whose ultimate capacity will be exceeded in a moderate earthquake and, if it
were to collapse, would likely result in injury or death or damage to another property. A moderate earthquake is
defined as approximately one-third as strong but of the same duration as the earthquake shaking assumed in
the design of a new building.
The official determination of whether or not a building is Earthquake-Prone is the responsibility of the relevant
Territorial Authority (TA). The earthquake rating resulting from an engineering assessment is only one, albeit
significant, aspect considered by the TA in making their determination. If the TA determines a building to be
Earthquake-prone, it will issue an EPB notice for the building and include it on the EPB register. The Building
(Earthquake-prone Buildings) Amendment Act 2016 then defines timeframes within which the owner must carry
out building work (i.e. upgrade or demolish) to ensure the building is no longer Earthquake-prone. These
timeframes range from 7.5 years to 35 years depending on the building type (priority or normal) and location
(high, medium or low risk areas).
The Building (Specified Systems, Change the Use, and Earthquake-prone Buildings) Regulations 2017 made
significant changes to the system for identifying and remediating Earthquake-prone buildings. These include:
� providing an operational basis for identifying earthquake-prone buildings – the EPB Methodology
� new definitions for key terms including ‘Earthquake-prone Buildings’ and ‘ultimate capacity’
� a requirement to categorise Earthquake-prone Buildings in terms of their earthquake rating
� providing a national-based system in place of individual earthquake-prone building policies for each TA
The Technical Guidelines document used by engineers to carry out seismic assessments is an integral part of
the EPB Methodology.
In addition, the New Zealand Society for Earthquake Engineering (NZSEE) define a building with a seismic
rating less than 67%NBS as an Earthquake-Risk Building (ERB), and recommend a minimum target
strengthening level of 67%NBS.
It is considered impractical and unaffordable to design every building to withstand the largest earthquake
imaginable. Consequently, with respect to the determination of design loads for natural hazards, the New
Zealand Loading Standard adopts a probabilistic approach that takes into account the exposure hazard at a
given location, along with factors such as building importance.
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Thus, the Loading Standard may be said to adopt a risk management approach in setting the loading levels that
a given building is required to withstand.
For Importance Level 3 (IL3) buildings (e.g. structures that may contain people in crowds), the “design”
earthquake load is set at the 1 in 1000 year return period earthquake event. This event has approximately a 5%
probability of exceedance over the assumed 50 year life of a building.
Assessment Methodology
We have adopted a stepped analysis approach to undertaking the seismic assessment of the Sir Howard
Morrison building starting with simpler analysis methods and progressively employing more sophisticated
methods of analysis and calculations to determine the seismic rating of the building. The techniques used are
generally as outlined in the guideline document The Seismic Assessment of Existing Buildings - Technical
Guidelines for Engineering Assessments, dated July 2017 (the Engineering Assessment Guidelines). Previous
versions of this guideline document were referred to as the NZSEE Guidelines, as they were produced by the
New Zealand Society for Earthquake Engineering. The guidelines have now been fully revised, with the new
version produced by three technical engineering societies (NZSEE, the Structural Engineering Society
(SESOC) and NZ Geotechnical Society (NZGS)), in conjunction with the Ministry of Business, Innovation and
Employment (MBIE) and the Earthquake Commission (EQC).
Our methodology is briefly summarised below, which generally follows the key steps of the Simple Lateral
Mechanism Analysis (SLaMA) technique described in Chapter 2 and Appendix 2A of the Engineering
Assessment Guidelines:
� Review of the available structural drawings to identify the main structural elements and any apparent
“structural weaknesses” of the building.
� Visual inspection of the building including the general presence and arrangement of the structures and
additions, the concrete frames, shear walls, stairs and relationship to adjacent buildings, carried out between
the 22nd June and 19th September 2017 by Beca structural engineers, including identification of non-
structural elements that may present a significant life-safety hazard.
� Selection of appropriate member properties and determination of structural element probable capacities.
� Calculation of the expected seismic actions on the building following the current New Zealand loading
standards (NZS1170).
� Hand analysis of selected key elements of the building to determine the likely failure mechanisms of these
subassemblies, and the whole building.
� Development of an elastic three-dimensional (3D) ETABS computer model of the building for analysis of the
force distributions.
� Development of elastic two-dimensional (2D) computer models for the analysis of key structural elements.
� Undertake a qualitative assessment of potential geo-hazards e.g. liquefaction, lateral spreading, slope
instability and their consequence of the performance of the structural system.
� Determination of the likely seismic rating of the building compared with an equivalent new building at the site
based on our inspections, the structural weaknesses identified, our calculations, and our engineering
judgment.
Explanatory Statement
� This report has been prepared by Beca at the request of our Client and is exclusively for our Client’s use for
the purpose for which it is intended in accordance with the agreed scope of work. Beca accepts no
responsibility or liability to any third party for any loss or damage whatsoever arising out of the use of or
reliance on this report by that party or any party other than our Client.
� The inspections of the building discussed in this report have been undertaken to assist in the structural
assessment of the building structure for seismic loads only. This assessment does not consider gravity or
wind loading or cover building services or fire safety systems, or the building finishes, glazing system or the
weather tightness envelope.
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� This assessment does not include an assessment of the building condition or repairs that may be required.
� No geotechnical ground investigations, subsurface or slope stability assessments have been undertaken.
Geotechnical input to the assessment has been based on a desktop review of readily available information
about the site and general area.
� Beca is not able to give any warranty or guarantee that all possible damage, defects, conditions or qualities
have been identified. The work done by Beca and the advice given is therefore on a reasonable endeavours
basis.
� Except to the extent that Beca expressly indicates in the report, no assessment has been made to determine
whether or not the building complies with the building codes or other relevant codes, standards, guidelines,
legislation, plans, etc.
� The assessment is based on the information available to Beca at the time of the assessment and assumes
the construction drawings supplied are an accurate record of the building. Further information may affect the
results and conclusion of this assessment. The information used to undertake the seismic assessment is
listed in Appendix A.
� Beca has not considered any environmental matters and accepts no liability, whether in contract, tort, or
otherwise for any environmental issues.
� The basis of Beca’s advice and our responsibility to our Client is set out above and in the terms of
engagement with our Client.
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2 Building Description
General
Summary information about the building is presented in the following table. Reference Information used to
undertake this seismic assessment is listed in Appendix A.
Table 2: Building summary information
Item Details Comment
Building name Sir Howard Morrison Performing Arts Centre (SHMPAC)
Street Address 1170 Fenton Street, Rotorua
Age 79 years, Original structure constructed in 1938
There have been multiple additions to the original building since 1938, however most of the original building remains.
No condition assessment has been undertaken in this DSA
Description / Building Occupancy SHMPAC includes an Auditorium, Fly Tower, Concert Hall, Dressing areas, office space, Storage areas, Function Room, Supper Room, Kitchen, Foyer and Plant Room.
Importance Level 3 (except IL2 for the stair adjacent to the Concert Hall, Transformer and Boiler House)
More than 300 people can congregate in one area.
Site sub soil class Primarily structure: D
Parts: C
Note: The previous high-level assessment was based on a site sub-soil class C. Since the high-level assessment, further geotechnical data has been made available, suggesting site sub-soil class D. Consequently we have adopted the more onerous soil class.
Building Footprint / Floor Area Approximately 3400m2
No. of storeys / basements Typically one and two storey building, with a three storey Fly Tower.
Structural system Refer to Section 2.5. Structural systems differ for different structures that make up the building.
Earthquake resisting system Predominantly concrete frame or shear walls, with the exception of the fly tower which is a steel braced lattice structure. Refer to Section 2.5.
Earthquake resisting systems differ for different structures that make up the building.
Foundation system Typically, shallow concrete pads and ground beams
Stair system Precast, in-situ concrete, and steel
Other notable features Canopy at the front of the building on western side, and canopy on the south western side.
Past seismic strengthening Strengthening including addition of shotcrete to some pumice concrete walls and strengthening of some connections.
Minimal strengthening to connections and shotcrete on walls undertaken in 1993
Temporary props installed June 2017
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Item Details Comment
Temporary props installed to support concrete columns in the Concert Hall.
Construction information Structural drawings Drawings provided by Rotorua Lakes Council, including the original Rotorua Borough Council drawings, Sigma, and Works.
Likely Design Standards NZSS95:1935, NZSS1900:1965, NZS4203:1976, NZS3101: 1982, NZS4203:1984, NZS4203 1992: NZS4203: 1994, NZS1170:2004
Heritage Status Historic Place Category 1.
Other
Figure 2: Plan of the building showing construction date of different sections
Photographs of the building are included in Appendix D.
Heritage status
The building is listed by the Heritage New Zealand as a ‘Historic Place Category 1’.
Detailed Seismic Assessment – Sir Howard Morrison Performing Arts Centre
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Geotechnical Considerations
2.3.1 Historical Information
Our desktop assessment has considered the following sources of information:
� Published Geological Map of the Rotorua area (GNS, 2010)
� Terrane (2009) and Works Consultancy (1993) reports on the SHMPAC
� Works Consultancy (1993) report on the neighbouring Civic Buildings
� Coffey (2015) report on the neighbouring Rotorua Tourism Centre and our Beca (2015) peer review of the
same
� Terrane (2014) geotechnical IEP assessment for the Rotorua Tourism Centre
� BSK (2006) detailed seismic assessment for the Rotorua Public Library
� Opus (2006, 2012) reports on the neighbouring Rotorua Police Station
� Bay of Plenty Regional Council (BoPRC) groundwater and geothermal bore data.
2.3.2 Summary of Historical Advice
Two geotechnical reports have been provided which detail assessments for alterations of the SHMPAC in
relation to the original 1930s and 1970s parts of the building. The key points from these reports are
summarised below.
� Works Consultancy (1993)
– The site is located within the Rotorua Caldera and underlain by alluvium of Holocene age consisting of
pumiceous sands and fine gravels with beds of soft to firm clay.
– The consolidation of soft clay layers may induce settlements of up to 90mm for pad and strip foundations.
� Terrane (2009)
– Site investigations measured groundwater at 3.5m below ground level (bgl).
– A peak seismic ground acceleration of 0.415g was adopted in the design which was noted to correspond
to a 1/1000 APE for an Importance Level 3 (IL3) building.
– The recommended site subsoil category for seismic design actions was taken as Class C based on NZS
1170.5:2004.
– Under the design criteria adopted in the assessment, liquefaction was not considered to be an issue for
structures at this site.
– The consolidation of soft clay layers may induce settlements of up to 30mm for pad foundations.
We note the available data suggests some variability in the ground conditions is likely across the building
footprint.
2.3.3 Current View of Liquefaction Potential
The current state of knowledge with regards to understanding liquefaction potential at the site and surrounding
area has advanced since the Terrane (2009) report. Liquefaction potential and the conditions that may trigger
liquefaction are now better understood and the recommendations provided in the original Terrane (2009) report
are no longer considered current.
We have undertaken a quantitative liquefaction assessment for this site utilising data from Coffey (2015) for the
nearby Rotorua Library and the NZGS/MBIE Guidelines for Earthquake Geotechnical Engineering Practice
(2016).
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2.3.4 Geohazards at the Site
Potential geohazards that we have identified that could affect the site are summarised in Table 3 below.
Table 3: Potential Geohazards
Potential Geohazard Hazard Comment
Liquefaction High risk Liquefaction can have a number of effects that require consideration for this DSA. These effects may include:
� Settlement/differential settlement,
� Cyclic ground movements,
� Increased cyclic deflections of foundations
� Lateral spread, and
� Reduction in bearing capacity
Collapse of Hydrothermally Altered Soil/Rock
High risk The failure of hydrothermally altered materials due to seismic shaking can have similar effects on a site as that of liquefaction. These effects may include:
� Settlement/differential settlement,
� Reduction in bearing capacity
Fault Rupture Very low risk No known active faults in the vicinity of the site
Slope Instability N/A
The site is located on an area of open and relatively flat ground
Rockfall N/A No rock-fall sources nearby
Landslide Dam-Break Flood N/A No dams located upstream
Dam Break N/A No dams located upstream
Tsunami N/A The site is not located near a coastline
The principal geohazards at this site are liquefaction and collapse of hydrothermally altered materials;
specifically, the differential settlement associated with these hazards. Settlement effects as a result of
liquefaction can be either free field (affecting the general area,) or can be in specific response to the static or
cyclic loads applied by the structure. The collapse of hydrothermally altered soils will likely result in subsidence.
Other Geohazards noted in Table 3 are unlikely to occur at this site.
2.3.5 2017 Geotechnical Detailed Seismic Assessment
2.3.5.1 Current Focus
The focus of a DSA is the potential for a step change in the structural system, giving rise to a life safety risk.
Serviceability concerns are not the main focus of a DSA, however recommendations for further work to address
potential damage limitation or serviceability concerns are discussed in Section 2.3.6.
2.3.5.2 Current Site Soil Class
SHMPAC is located within an area of lake deposits and lies within the Government Gardens area of geothermal
activity. The soils in the area are likely to be hydrothermally altered and therefore weakened by geothermal
weathering.
Geotechnical site investigations obtained from the historical information extend at most to 35m depth and do
not encounter rock. Groundwater bores within the area, which are not reliable for geological descriptions,
suggest that rock may lie at 50-60m bgl. This information suggests that a site subsoil Class of C (shallow soil
site) is highly unlikely. For this DSA we recommend classifying the site as Class D (deep soil site). Although an
intermediate classification between Class C and Class D is possible, further research and physical
investigations in regards to the depth to rock and the shear wave velocities of the overlying soils are required to
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determine the site class with certainty in accordance with the requirements set out in NZS1170.5:2004
incorporating Amendment 1.
2.3.5.3 Liquefaction Potential
The Ultimate Limit State (ULS) earthquake, for an Importance level (IL) 3 building, with a 50 year design
working life has an Annual Probability of Exceedance (APE) of 1/1000. This corresponds to a Peak Ground
Acceleration (PGA) of 0.39g for soil class D with a representative magnitude of 6.0 (determined from NZTA
Bridge Manual 3rd ed in accordance with NZGS Module 1) (NZTA, 2016).
We have undertaken a liquefaction assessment using the existing Coffey (2015) Cone Penetration Test (CPT)
data, noting that the available data is located around the neighbouring Rotorua Tourism Centre. Our
assessment indicates that the ground may experience localised liquefaction/softening in an event exceeding
1/175 APE (0.17g or 43% of ULS) with widespread liquefaction anticipated in events with an APE of greater
than 1/250 APE (0.20g or 51% of ULS).
We therefore recommend that the DSA assume liquefaction will initiate at shaking levels of approximately 50%
of ULS (IL3).
Based on the reported performance of low rise, shallow founded buildings supported on level ground subject to
liquefaction, the following consequence of liquefaction could be anticipated:
� Differential settlement of heavily loaded foundations and lightly loaded floors/aprons etc.
� Differential settlement associated with variations in the ground conditions across the site.
� Differential settlement between the concert wing and meeting room wing.
� Buoyancy effects on light, deeply embedded elements (e.g. the orchestra pit).
� Significant ‘softening’ of foundation response leading to rocking and ratcheting (vertically and rotationally) of
heavily loaded foundations.
Based on observations from Christchurch, the above effects may lead to differential settlements of several
hundreds of millimetres between foundation elements that are not well tied together.
The system performance of the Performing Arts Centre is currently assumed to be structurally dominated in
accordance with Part C4 of the Guideline for the seismic assessment of buildings (NZSEE, 2017).
2.3.5.4 Hydrothermally Altered Soil and Rock
SHMPAC is located within the Government Gardens area of geothermal activity. The soils in the area are likely
to be hydrothermally altered and therefore weakened by geothermal weathering. The historical information we
have reviewed suggests that the level of hydrothermal alteration begins at approximately 2m bgl.
Geothermal systems are developed by the transportation of water, at times acidic, down through the underlying
soils which is then heated by geologic processes (e.g. deep magma) before rising back toward the surface. As
the water moves, it dissolves minerals resulting in a porous and weakened structure. This fragile microfabric
may collapse or crumble under seismic shaking, which could result in subsidence beneath the foundations of
the building.
The sensitivity of hydrothermally altered soils to levels of seismic shaking is not known and could occur either
before or after liquefaction. The level of subsidence likely to result from such a collapse is unknown.
2.3.6 Recommendations for Future Assessments
We recommend additional testing be undertaken around the building to supplement any future assessment, and
to assist with the confirmation of site class (if required).
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Building Design
The first unified national loading and building design standard, NZSS95:1935 Model Building By-Law, was
introduced following the catastrophic 1931 Napier earthquake. This code required the building to be designed
for a nominal lateral force applied uniformly up the building. A revision to the loading and building design
standard was made in 1955, introducing minor improvements to reinforced concrete design.
There were significant changes to the knowledge base of structural engineers in the mid-1960s and the 1970s.
The NZS1900:1965 loading standard considered variations in regional seismicity and effects of dynamic
response in the calculation of seismic coefficients. Ductility requirements were introduced in NZS1900:1965,
but without clear guidance on how to achieve the ductility capacity.
Much research and development occurred in the late 1960s and early 1970s. Research and development in
New Zealand in the 1970s set the early benchmark for the design and detailing of ductile reinforced concrete
structures to resist earthquake loading. These findings were incorporated into a new loadings code
NZS4203:1976 and a new concrete code NZS 3101:1982.
A ductile structure designed to modern codes is expected to be able to undergo relatively large displacements
without collapse. Ductile structures are also able to dissipate energy and resist repeated cycles of seismic loads
without excessive strength degradation. Buildings designed with these features provide a higher level of life
safety performance in severe earthquakes compared with other buildings without these features.
The current New Zealand standard for derivation of Earthquake Loads is NZS1170.5:2004 Structural Design
Actions Part 5: Earthquake actions – New Zealand. It, along with materials standards as mentioned above, is
significantly advanced from that which the original 1935 standard which SHMPAC was likely designed to. It is
therefore reasonable to expect that the older structures of the building are going to be deficient when assessed
against current building standards, in terms of basic strength, available ductility, resilience, basic code-
compliance etc.
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Structural Systems
Descriptions of the gravity structure as well as the primary lateral load resisting systems for each structure that
form the Sir Howard Morrison Performing Arts Centre are identified below;
Table 4: Structural systems that form SHMPAC
Structure Gravity Structure Lateral Resisting System
Concert Hall � Timber-framed roof supported by
reinforced concrete columns framing onto
pad foundations.
� Heavy reinforced pumice concrete infill
walls spanning between columns.
� North-south direction is reinforced concrete
framing comprising of cantilever columns
and tie beam and pad foundations to most
but not all grids.
� Three of the north-south frames are integral
with the Auditorium structural framing.
� East-west direction reinforced concrete
framing and infill.
� Reinforced pumice concrete infill between
concrete frames on all wall lines except the
west elevation which has shotcrete
strengthened pumice concrete block infill
walls.
� Timber roof comprising of laminated roof
beams, timber purlins and ‘straight’ sarking
(perpendicular to north and south walls).
� Laminated roof beams bolted to the main
auditorium columns, ‘fishtailed’ anchor bolts
to the reinforced concrete columns
elsewhere.
Supper Room � Open plan single storey structure
� Timber framed roof which is supported on
concrete columns and pumice concrete
cavity block infill.
� Internal timber-framed, plasterboard lined
partitions/walls.
� Concrete walls around internal kitchen
area
� Reinforced concrete framing and infill
pumice concrete blocks north-south. All
north-south frames are integral with the main
auditorium structural framing.
� Reinforced concrete framing and infill
pumice concrete blocks east-west (south
elevation)
� Timber roof comprising of laminated roof
beams, timber purlins and ‘straight’ sarking.
� Laminated roof beams bolted to the main
auditorium columns, ‘fishtailed’ anchor bolts
to the southern reinforced concrete columns.
� East and south elevations have pumice
concrete cavity block infill walls
� North (Auditorium) and west (Concert Hall)
elevations have reinforced pumice concrete
infill walls.
� The west and south elevations have
reinforced pumice concrete infill walls.
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Structure Gravity Structure Lateral Resisting System
North-West Wing � Two-storey structure designed as part of
the original building.
� Timber-framed roof installed over the
original in 1950 additions.
� Roof supported on concrete frame.
� Some heavy walls including reinforced
concrete and pumice concrete cavity
block.
� First level reinforced concrete floor
continuous with North-East Wing.
� In-situ reinforced concrete stair.
� Reinforced concrete shear walls in both
directions. Longitudinally on grids B and D,
and transversely on grids 11 and 18.
� Reinforced concrete columns and beams
framing in both directions
� Cavity block infill with shotcrete overlay
strengthening on the east and west walls
and polyplast strengthening on the north and
south walls.
� Cast in-situ reinforced concrete first floor
diaphragm.
� Timber roof comprising of laminated roof
beams, timber purlins and ‘straight’ sarking.
� Laminated roof beams have limited capacity
‘fishtailed’ anchor bolts to the reinforced
concrete columns.
� The two eastern most grids (grid 11 and 13)
are integral with the main auditorium
structural framing. Concrete moment frame
and shear walls in north-south Direction on
both levels.
North-East Wing � Originally a single-storey structure with a
second storey added in 1950 alterations.
The single level structure is continuous
with the North-West Wing.
� Light-weight roof with steel trusses and
timber frame added in 1993 over original
roof structure.
� Concrete frames at both upper and lower
levels.
� First level reinforced concrete floor
continuous with North-West Wing
� Pumice concrete block walls between
concrete frames.
� Shear wall dominant in both directions.
In the longitudinal direction the North-
East Wing is tied into the Auditorium
and Plant Room/Kitchen shear walls,
and transversely is tied into the Plant
Room/Kitchen shear walls.
� Reinforced concrete column and beam
framing in both directions at ground level.
� Reinforced concrete column and beam
framing in both directions at first floor level,
however the upper level was an addition in
the 1950’s and appears to be pinned to the
lower frame.
� Cast in-situ reinforced concrete first floor
diaphragm.
� All north-south grid framing is integral with
the main auditorium structural framing.
� The original roof does not have sarking or
bracing but the 1993 addition has a plywood
diaphragm.
� Steel truss connections comprise of bolted
and welded fixings to the auditorium steel
columns and cast-in anchor bolts to the
northern first floor columns.
� Upper storey framing has reinforced
concrete infill to north and east elevations.
� There is no continuously sarked diaphragm
at the same level as the North-West Wing.
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Structure Gravity Structure Lateral Resisting System
Auditorium � Lightweight roof with bolted steel roof
trusses.
� Heavy ceiling with a mass of cables
particularly at the eastern end of the
Auditorium, and lighting hangers.
� Concrete encased steel columns and
beams.
� Reinforced concrete wall infill to north
and south elevations.
� Concrete in-situ mezzanine and projector
room floor slabs with concrete encased
steel beams.
� North-south direction has steel (concrete
encased) columns and a roof truss creating
a frame.
� East-west direction has steel encased
columns and beams with reinforced concrete
infill providing shear wall behaviour.
� The roof has ‘straight’ sarking to achieve
diaphragm action, but is not continuous over
the length of the auditorium.
Fly Tower � Three storey structure designed as an
extension to the original auditorium.
� Lightweight steel and timber roof
� Concrete wall on the east elevation
� Foundations comprise of concrete ground
beams below main framing in both
directions.
� North –south direction has reinforced
concrete shear wall on the east side and a
braced portal frame on the west elevation.
� East-west direction has steel tension only
cross bracing (Reid) up the full height.
� On the east elevation the fly tower is integral
with the back of house dressing room.
� The fly tower is predominantly a steel braced
lattice structure.
East Dressing
Room
� Two storey structure designed as an
extension to the original Auditorium
� Concrete wall on the west elevation
� Floors at first and second level are
precast concrete units with cast in-situ
topping.
� Foundations comprise of concrete ground
beams below main framing in both
directions.
� North –south direction has a reinforced
concrete shear wall on the west elevation.
� East-west direction has reinforced concrete
moment frames, and shear walls located
either side of central stair.
� Reinforced concrete floor diaphragms on the
first and second level of the dressing room.
� The east dressing room is integral with the
fly tower on the west elevation.
Storage Room � Heavy reinforced concrete walls in both
directions
� Light weight roof with timber rafters.
� The mezzanine level is support by a steel
gravity structure connected into the
reinforced concrete shear walls.
� Heavy reinforced concrete shear walls in
both directions
Foyer � Light weight roof with steel trusses
supported on concrete columns
� Concrete columns provide support in both
directions as cantilevers fixed at the base in
one direction and moment frame in the other
direction (footing follows curve of arc).
Kitchen/Plant Room � Heavy reinforced concrete shear walls in
both directions
� Heavy reinforced concrete shear walls in
both directions
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Structure Gravity Structure Lateral Resisting System
Function Room � Light weight roof with steel trusses
supported on concrete columns
� Concrete columns provide support in both
directions as cantilevers fixed at the base in
one direction and moment frame in the other
direction (footing follows curve of arc).
South-West Stair � Reinforced concrete (RC) stairs
supported on RC walls on the east and
west elevations on shallow foundations
and columns
� North-south direction has reinforced
concrete shear walls.
� East-west direction relies on frame action
provided by RC columns and beams,
coupled with the stair flights.
Transformer / Boiler
House
� Light-weight timber-framed roof
supported on reinforced masonry block
walls on shallow foundations.
� Both directions have reinforced masonry
block shear walls.
3 Results of Seismic Assessment
The results of our quantitative seismic assessment indicate the building’s earthquake rating to be less than
34%NBS (at IL3).
Table 5 presents the evaluated seismic performance in terms of %NBS of each individual structure in each
loading direction.
Table 5: Summary of seismic score for areas <67%NBS (IL3)
System Direction %NBS Failure
type
Notes
Foyer Truss Transverse (N-S
direction)
25%NBS Ductile Buckling of the bottom chord. Sensitive to
soil-structure interaction effects and
interaction between the north and south
wings.
Supper
Room/Kitchenette
walls
Both directions
25%NBS Brittle Unreinforced concrete block wall out of plane, and a suspended unreinforced pumice concrete block wall with no reliable load path.
Storage Room Transverse (N-S)
directions
25%NBS Ductile
/Brittle
Reinforced concrete wall out-of-plane and
potential loss of gravity support to plant
support beams.
North Wing Frame Transverse (N-S)
directions
45%NBS Brittle Governed by the beam – column joint
detailing. Assuming no diaphragm or other
mitigating measures.
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System Direction %NBS Failure
type
Notes
Northeast Wing
Frame
Transverse (N-S)
direction
50%NBS Brittle Our calculations determined that ‘failure’ of
the roof truss, could occur at <34%NBS,
resulting in redistributed and alternate load
paths/ mechanisms being activated to
maintain roof support. The steel roof truss
fixings in combination with a lack of robust
diaphragm or roof bracing system, appear
to be particularly deficient.
Concert Hall
Frame
Transverse (N-S)
direction
30%NBS Ductile Buckling of the props. This is the result of
changing from Soil Class C to Soil Class D,
after prop design, based on further
geotechnical data being made available.
North/South Wing
end walls
Longitudinal (E-W )
direction
30%NBS Brittle Unreinforced pumice concrete block wall.
Invasive investigations suggest the outer
whythes are unsupported out of plane.
Supper Room
Walls
Longitudinal (E-W)
and Transverse (N-
S) directions
45%NBS Brittle Unreinforced pumice concrete block walls
out of plane.
North Wing Admin
Walls
Transverse (N-S)
directions
55%NBS Brittle Unreinforced pumice concrete block walls
out of plane.
Currently the walls have a Polyplast layer
for out of plane strength, however we don’t
consider this provides any substantial
increase in capacity.
Auditorium Transverse (N-S)
directions
50%NBS Ductile Frame governed by ultimate drift limits, due
to loss of frame action from roof trussed
diagonal member buckling.
Fly Tower Both directions 25%NBS Brittle Deficient Reid brace connectors at ends of
cross bracing, typical.
Transverse 32%NBS Brittle Potential for loss of gravity support to truss
over the proscenium arch.
Dressing Room Both directions 45%NBS Brittle The diaphragm capacity is limited by the
collector and tie capacities.
Function Room Both directions >90%NBS Ductile Our calculations determined that the roof
beams were the critical elements in the
frame and could resist levels of earthquake
shaking to at least 90% ULS (IL3).
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Primary Seismic System Limiting Mechanisms
The seismic rating of the Sir Howard Morrison Performing Arts Centre (SHMPAC) is limited by:
3.1.1 Foyer
The most limiting mechanism for this area of SHMPAC is identified as the foyer trusses on grids 14 and 15,
refer Figure 3 below. In particular, buckling of the bottom chord, potentially resulting in the collapse of the foyer
roof. We assessed these elements as approximately 25%NBS.
Another limiting mechanism for this area is the connection of the foyer truss to the north and south wings.
Under earthquake shaking at 67%NBS liquefaction is likely and large differential displacements between the
north and south wings may occur. As a result the bolted fixings between the trusses and walls/columns could
potentially pull out resulting in the foyer truss becoming unstable with no dependable lateral or vertical load
system.
Figure 3: Foyer trusses spanning between north and south wings
3.1.2 Supper/Kitchen walls
A limiting element in the Supper Room is the unreinforced pumice concrete block walls between the Supper
Room and the Kitchen and a suspended unreinforced pumice concrete block wall above the Kitchen. There is
currently significant cracking at the ends of these walls, suggesting only limited strength and unreliable load
paths. Under moderate shaking the suspended wall may lose vertical support, and the Supper Room/Kitchen
wall become unstable/collapse out of plane. These elements are only expected to be a localised life-safety risk
and not result in catastrophic collapse of the building. Refer to Figure 4 below for the location of these walls. We
assessed these elements as approximately 25%NBS.
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Figure 4: Location of critical Supper Room/Kitchen walls
3.1.3 Storage Room
A limiting element in the Storage room is the reinforced concrete walls on gridline L (south elevation). This wall
spans 13.4m horizontally with minimal support at roof level. Due to the lack of support and large span, the wall
is subject to large displacements. There is also a mezzanine structure supported by the storage room wall. The
mezzanine gravity structure is connected to the wall with 2-M12 bolts (embedment unknown) and can be
expected to only sustain minor deflections prior to failure. In addition to the risk of the wall falling out, there is a
significant risk the mezzanine structure supporting HVAC plant will lose gravity support. Refer to Figure 5 and
Figure 6 below for the location of this wall. We assessed the Storage room wall as approximately 25%NBS.
Figure 5: Storage Room wall - critical out of plane
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Figure 6: Mezzanine gravity support structure in the Storage Room
3.1.4 North Wing Frame – Grids 11 to 18
Based on our intrusive investigation findings for the similar Concert Hall structure, we have assumed there is no
dependable roof diaphragm connection to the North Wing walls. The limiting mechanism for the North Wing,
between grids 11 and 18 is the shear capacity of the beam-column joints in the transverse frame at first floor
level on grid 13. The deficiency of the beam-column joint means the frame cannot yield, and is potentially
subject to brittle failure. Under moderate shaking the transverse frame may be susceptible to significant shear
damage/failure in the joint area, potentially resulting in loss of gravity load bearing capacity in the column. Refer
to Figure 7 for an elevation of a transverse frame in the North Wing. We assessed the North wing frame on grid
13 as approximately 45%NBS. This is a lower bound based on the known deficiencies of this particular beam-
column joint.
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Figure 7: North wing transverse frame
3.1.5 North East Wing – Grids 7 - 11
The limiting mechanism for the North Wing, between grids 11 and 18 is the shear capacity of the bolts
connecting the top chord of the truss to the Gird B frame.
In the 1950’s an additional level was added to this area of the North Wing. Based on the available drawings
there is limited reinforcing that continues from the level. As a result the additional 1950’s frame is considered to
be pinned at the first floor level on the north elevation. On the south elevation, all framing is integral with the
Auditorium structural framing.
The performance of the North East Wing appears to be governed by the steel roof structure, including fixings
and northern wall out-of-plane capacity. Our calculations determined that the ‘failure’ of the fixings to the bottom
chord and roof components could occur at <34%NBS, resulting in redistribution and alternate load
paths/mechanisms being activated to maintain roof support. The steel truss roof fixings in combination with a
lack of a robust roof diaphragm or roof bracing system, appear to be particularly deficient.
Refer to Figure 8 and Figure 9 below for a typical elevation of these frames. We assessed the North-East Wing
frames between grids 7 and 11, based on the wall out-of-plane capacity following the failure of the above
elements as approximately 50%NBS.
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Figure 8: Elevation of the North Wing transverse frame
Figure 9: Indication of the trusses between grids 7 and 11 in the North Wing
3.1.6 Concert Hall
The significant limiting mechanism for the South Wing, between grids 11 and 18 is the buckling of the props in
the transverse frame. The props are a recent strengthening addition to the Concert Hall and were installed in
June 2017. Based on the geotechnical information at the time of this strengthening, the props were designed for
site subsoil class C. Additional geotechnical data obtained post June 2017 indicates the site sub soil class to be
D. The consequence of this soil class change results in an increase in earthquake loading of approximately
30%. Refer to Figure 10 below for location of props.
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Prior to the props being installed, the Concert Hall system was an upside down portal frame with the critical
element being the beam-column joint detailing.
During the invasive inspections we identified there was no connection between the roof diaphragm and the
north, south, and east walls. We have assumed based on this that the west wall also has no dependable
connection. As a result, our calculations are based on there being no roof diaphragm.
We assessed the South wing frames between grids 11 and 18 as approximately 25%NBS.
Figure 10: Location of props in the Concert Hall
3.1.7 North and South Wing end walls on grid 18
The limiting mechanism for the North and South Wing end walls, on grid 18, is the out of plane capacity of the
unreinforced pumice concrete blocks. Previously these end walls have been strengthened with 200mm of
reinforced concrete shotcrete. However, during the site inspections, it was noted that the dowel between the
shotcrete and pumice block was only embedded in the inner whythe of the block, leaving the outer whythe
susceptible to falling under earthquake shaking. We assessed the North and South wing pumice concrete
block infill walls on grid 18 as approximately 30%NBS.
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Figure 11: Concert Hall end wall on grid 18. North Wing end wall similar
3.1.8 Supper Room Walls – Grid H-K and Grid 7-11
The limiting mechanism for the South Wing (external Supper Room walls), between grids 7-11 (south elevation)
and grids H-K (east elevation) is the out of plane capacity of the infill unreinforced pumice concrete cavity
blocks. Under earthquake shaking there is potential for the infill pumice concrete cavity blocks to fall out
creating a localised life-safety hazard. Refer to Figure 12 for the location of these walls. We assessed the
Supper Room walls between grids 7-11 and H-K as approximately 45%NBS.
Figure 12: Unreinforced infill pumice block walls around the Supper Room
3.1.9 North-West Wing Infill Walls – Grid 11-18
The limiting mechanism for the North Wing walls, between grids 11-18 is the out of plane capacity of the infill
pumice concrete cavity blocks on the first floor. Refer to Figure 13 below for an indication of the extent of cavity
blocks on the first floor in the North Wing. Under earthquake shaking there is potential for the infill pumice
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concrete cavity blocks to fall out creating a localised life safety hazard. We assessed the North Wing walls
between grids 11-18 as approximately 55%NBS.
Figure 13: Extent of cavity block wall on the first floor of the North Wing
3.1.10 Auditorium frames
Based on our intrusive investigation findings for the Concert Hall structure, we have assumed there is no
dependable roof diaphragm connection to the Auditorium walls. The limiting mechanism for the Auditorium
frames in the transverse direction is the hold down bolts at the base connection and roof level drift. During the
invasive investigations we identified the roof diaphragm is not continuous along the full length of the Auditorium.
Currently there is a large cut in the diaphragm at the western end that is approximately 400mm wide x 8000mm
long.
Our calculations determined that the failure of the truss diagonal could occur at relatively low levels of shaking
(<34%NBS), resulting in redistribution and alternative load paths/mechanisms being activated to maintain
structural integrity. The frames with the transverse seating beams are considered to be more resilient than
those at the eastern end of the Auditorium which only comprise of columns and roof beams (plus foundation tie
beams).Refer to Figure 14 for a typical elevation of the Auditorium truss. We assessed the Auditorium frames
as approximately 50%NBS.
Based on our intrusive investigation findings for the similar Concert Hall structure, we have assumed there is no
dependable diaphragm connection to the Auditorium walls.h
Figure 14: Auditorium truss
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3.1.11 Fly Tower
The limiting mechanism for the Fly Tower is the deficiency of the Reid brace (banana) end connectors. Recently
(Sept 2015) it has become clear, based on current available test data, that the Reid brace system is likely to fail
in a brittle manner, at the connector. Available design calculations for the Fly Tower, provided by RLC, indicate
that the system was designed considering, nominal ductility (µ=1.25), subsoil class C and importance level 2.
Our assessment checks are based on elastic loads (µ=1.0), sub-soil class D, and importance level 3. This
substantially increases the seismic demands.
Our calculations determined that a failure of the Reid brace system could occur at relatively low levels of
shaking (25%NBS), potentially resulting in the collapse of the Fly Tower, and loss of lateral stability of the back
of house dressing room. In addition, the truss above the proscenium arch (truss 4, refer to Figure 15, Truss “4”)
appears to be designed to support gravity loads only. We have considered the support of this truss as a result
of the lateral loading induced by displacement of the fly tower. It is possible that the vertical columns denoted ‘F’
at approximate third points may act to support the truss should the end connections fail. However, the original
drawings do not provide these connection details and these were not viewed on site to confirm this. Without
confirmation of this, our assessment assumes that failure of the end connections may result in collapse of the
truss. On this basis, the fly tower truss has a score of 32%NBS based on the shear capacity of the truss end
connections. Although note, this is not the critical element.
Refer to Figure 15 for west elevation of the Fly Tower. We assessed the Fly Tower as approximately 25%NBS.
Figure 15: West elevation of the Fly Tower
3.1.12 Dressing Room / Back of House
The limiting mechanism for the Dressing Room is the first and second floor diaphragms. The diaphragms
comprise of precast floor units with in-situ topping reinforced with brittle non-ductile mesh. Under earthquake
shaking there is potential for premature diaphragm damage due to the brittle mesh reinforcement. We
assessed the Dressing Room / Back-of-House as approximately 45%NBS.
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Figure 16 below is an indication of the location of the elements/areas that obtain a %NBS score less than
34%NBS and less than 67%NBS
Figure 16: Overall indication of the areas that score below 34%NBS and 67%NBS
Staircase and Safe Egress
The Department of Building and Housing issued Practice Advisory 13 in response to concerns about stair
collapse and damage observed in the Christchurch earthquake. The primary concern of this Practice Advisory
is staircases with sliding support details in mid to high-rise multi-storey buildings.
There are six main stair cases in the building, as shown in Figure 17. There are no known sliding support
details for these stairs. The Fly Tower stair cases are of steel-framed construction with steel grating treads. All
other are reinforced concrete construction adjacent to, or supported by shear walls. Our assessment of each of
the main stairs is summarised in Table 6 below.
Detailed Seismic Assessment – Sir Howard Morrison Performing Arts Centre
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Figure 17 Floor plan of SHMPAC showing main stair locations
Table 6 Stair assessment summary
Ref # Stair Locations Original Drawing Description and Assessment
1 Main Foyer
A reinforced concrete (RC) stair tied to floor slabs at the top and bottom. Provides main access and egress to and from the Auditorium.
Supported on RC shear walls which provide both gravity and lateral support.
The lateral stair support system has displacement compatibility with the primary supporting structures and therefore considered not to pose a significant life-safety hazard.
2 Dressing Room
A RC stair tied to floor slabs at the top and bottom. Provides main access and egress between the stage and dressing room floors.
Supported on RC beams at each end, and located adjacent to RC shear walls.
Located next to a shear wall, so differential displacements between landings will be limited. Therefore the stair is considered not to pose a significant life-safety hazard.
Detailed Seismic Assessment – Sir Howard Morrison Performing Arts Centre
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Ref # Stair Locations Original Drawing Description and Assessment
3 Fly Tower - South
A steel stair connected to concrete floor slabs and steel-framed landings. Provides service access between the stage and Fly Tower upper levels.
A relatively flexible stair system, supported on steel framing at one end, and used for service access only. Therefore the stair is considered not to pose a significant life-safety hazard.
4 Fly tower - North
As for stair # 3.
5 Auditorium Egress
A RC stair tied to a floor slab at the top and ground at the base. Provides main egress from the Auditorium, and access to the plant room.
Supported on an RC beam at the top, an RC wall at mid-landing, and ground beam on-grade and the base. Located adjacent to a RC shear wall.
Located next to a shear wall and not restrained at the base or mid-landing. Therefore the stair is considered not to pose a significant life-safety hazard.
6 North Wing - Admin
A RC stair tied to floor slabs at the top and bottom. Provides egress from the Admin area to outside.
Supported on RC beams at each end, and located adjacent to RC shear walls.
Located next to a shear wall, so differential displacements between landings will be limited. Therefore the stair is considered not to pose a significant life-safety hazard.
7 South Concert Hall
A disused RC stair structure separated from the Concert Hall. Tied to RC slab landings and walls at the end of each flight.
Considered not to pose a significant life-safety hazard.
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4 Commentary on Associated Seismic Risks
Risks from Adjacent Buildings
SHMPAC is located in Rotorua’s CBD. Recent experience in Christchurch indicates that even if a building
performs well in a significant earthquake the impact of other adjacent and relatively close buildings may
affect whether it can be used in the immediate post-earthquake environment. SHMPAC is a standalone
building with the only building in close proximity being the Rotorua Lakes Council office building. In an
earthquake this may pose a risk to SHMPAC’ seismic vulnerability and accessibility.
Risks from Non-structural Building Elements
From our recent experience in evaluating similar buildings in Christchurch, non-structural building elements
(façade glass, ceilings, internal walls, overhead services) constitute a significant portion of the repair /
reinstatement cost following an earthquake. In a moderate seismic event, non-structural element damage
will likely contribute heavily to downtime and the repair costs.
For a new building, full-height partitions (glazed or Gib-board lining), glazed street facades and ceilings are
normally designed to accommodate the building’s deformations.
Concerns at SHMPAC in a significant seismic event include;
� The potential for the ceiling tiles in many of the different sections of the building to fall out of ceiling
frames.
� The potential for the large glass panels in the Foyer and the Function Room to be damaged.
� The potential for the heavy ceiling in the Auditorium to fall down.
We have not investigated the available deformation capacity of these elements as it is beyond the scope of
this report.
5 Assessment of Seismic Risk
Seismic Risk and Performance Levels
Our quantitative seismic assessment of the Sir Howard Morrison Performing Arts Centre indicates an
earthquake rating of less than 34%NBS (at IL3). The building has been assessed in accordance with the
guideline document The Assessment of existing Buildings – Technical Guidelines for Engineering
Assessments , dated July 2017 (Engineering Assessment Guidelines). The assessment result is based on
an Importance Level 3 (IL3) building, in accordance with the joint Australian/New Zealand Standard –
Structural Design Actions Part 0, AS/NZS 1170.0:2002 as being deemed appropriate for this building.
Therefore, the building is a Grade D building, following the Engineering Assessment Guidelines building
grading scheme. Grade D buildings represent a life-safety risk to occupants comparable to 10-25 times that
expected for a new building, indicating a high risk exposure.
The New Building Standard requires an IL3 building to have a low probability of collapse in a 1 in 1000-year
“design level” earthquake (i.e. an earthquake with a probability of exceedance of approximately 5% over the
assumed 50 year design life of a building).
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Relative Earthquake Risk
Building Grade Percentage of New Building
Strength (%NBS)
Approx. Risk Relative to a New
Building
Risk Description
A+ >100 <1 low risk
A 80 to 100 1 to 2 times low risk
B 67 to 80 2 to 5 times low to medium risk
C 33 to 67 5 to 10 times medium risk
D 20 to 33 10 to 25 times high risk
E <20 more than 25 times very high risk
A building with an earthquake rating less than 34%NBS fulfils one of the requirements for the Territorial
Authority to consider it to be an Earthquake-Prone Building (EPB) in terms of the Building Act 2004. A
building rating less than 67%NBS is considered as an Earthquake Risk Building (ERB) by the New Zealand
Society for Earthquake Engineering.
Since SHMPAC is currently less than 34%NBS, Rotorua Lakes Council may determine the buildings status
as earthquake prone. If it does so, RLC will also issue an EPB notice for the building and include it on the
EQB register.
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6 Next Steps
Since the seismic rating is less than 34%NBS, further action is required to meet the regulatory minimum
requirements set out in the Building (Earthquake-prone Buildings) Amendment Act 2016. We recommend
Rotorua Lakes Council consider carrying out the following next steps:
� Review the concept seismic strengthening schemes and associated cost estimate provided in a separate
cost report.
� Consult with their Heritage Architect in relation to the concept strengthening schemes proposed.
Coordinate any other upgrade works proposed to the building.
� Undertake detailed design of the strengthening scheme and documentation for Building Consent
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Sources of Information The following information was used to undertake the seismic assessment:
� Documents obtained from Rotorua Lakes Council comprising of scanned original structural drawings and
design calculations from different stages of construction, some original construction photographs, and
some geotechnical reports for SHMPAC and the surrounding area.
� Beca’s Seismic Assessment Review Report dated 28 April 2015 and Concept Seismic Strengthening
Targeting 67%NBS Report dated 23 January 2017.
� External and internal visual inspections of the building carried out by Beca between the 22nd June 2017
and 19th September 2017.
� Intrusive investigation findings such as concrete strengths, extent of diaphragms and presence of
reinforcing steel in concrete elements.
The following documents and references were available to undertake the seismic assessment:
� New Zealand Standard NZS1170 “Structural Design Actions”.
� New Zealand Standard NZS3101:2006 “Concrete Structures Standard”.
� New Zealand Standard NZS3404:1997 “Steel Structures Standard”.
� The Seismic Assessment of Existing Buildings - Technical Guidelines for Engineering Assessments,
dated July 2017.
PAGE 1 OF 7 www.opus.co.nz
Opus International Consultants Ltd
P +64 4 587 0600
Opus Research
33 The Esplanade, Petone
PO Box 30 845, Lower Hutt 5040
New Zealand
25 October 2017
Craig Lavin
Beca Infrastructure Ltd
P O Box 903
Tauranga 3140
Ref: 524A17.00
Sir Howard Morrison Performing Arts Centre – Concrete Core Strength Results
Dear Craig
1. Introduction The seismic performance of the Sir Howard Morrison Performing Arts Centre (SHMPAC) in Rotorua is
currently being assessed and as part of that assessment the strength of the concrete was required to be
measured. Cores for concrete strength determination were delivered to Opus Research on 12 October
then tested on 24 October 2017. This letter reports the results of that testing.
2. Samples Twenty four nominally 84mm diameter concrete cores were removed from a variety of locations in the
SHMPAC building. A general description of the cores delivered is presented in Table 1. Representative
photos of each core type are presented in Figures 1 to 8.
Four cores were assessed to be unsuitable for compressive strength testing:
C1 (iii) – reinforcing bar cavity through the middle of the core.
C2 (ii) – core length less than diameter.
S1 (iii) – plastic conduit across core diameter.
S3 (iii) - core length less than diameter.
Twenty cores were subsequently tested for compressive strength.
PAGE 2 OF 7 www.opus.co.nz
Table 1: General Description of Cores
Core Identifier Concrete Description
C1
(i, ii, iii)
Concrete contains crushed volcanic aggregate with a maximum size of about
20mm but generally about 12mm. Concrete well compacted but appears
porous.
C2
(i, ii, iii)
Concrete contains rounded greywacke aggregate with a maximum size of
about 20mm. Concrete is well compacted.
S1
(i, ii, iii)
Concrete contains rounded greywacke aggregate with a maximum size of
about 20mm. Concrete is well compacted.
S2
(i, ii, iii)
Concrete contains crushed volcanic aggregate with a maximum size of about
20mm but generally about 12mm.
S3
(i, ii, iii)
Concrete contains crushed volcanic aggregate with a maximum size of about
20mm but generally about 12mm.
W1
(i, ii, iii)
Concrete contains crushed pumice aggregate with a maximum size of about
15mm but generally about 10mm. Concrete is well compacted.
W2
(i, ii, iii)
Concrete contains crushed volcanic aggregate with a maximum size of about
25mm. Concrete is well compacted.
W3
(i, ii, iii)
Concrete contains crushed pumice aggregate with a maximum size of about
15mm but generally about 10mm. Concrete is well compacted.
3. Methodology The core ends were first trimmed with a wet cut diamond saw.
The compressive strength of the concrete core samples was measured in accordance with Section 9
Determination of Strength in Compression of Drilled Cores from NZS 3112: Part 2 Tests Relating to the
Determination of Strength of Concrete. The cores were tested in the ‘dry’ state, i.e. stored in air at room
temperature for 7 days before testing at the completion of all preparation activities. This procedure was
chosen to represent the moisture condition of the concrete in the building.
The preferred length to diameter ratio for concrete core testing is 2:1 but this cannot always be achieved.
To account for this, when necessary the compressive strength was normalised to this aspect ratio using
the correction factors given in ASTM C 42 Standard Test Method for Obtaining and Testing Drilled Cores
and Sawed Beams of Concrete. The minimum length to diameter ratio allowed under this method is 1:1.
The core diameter preferred by NZS 3112 is 100mm for concrete containing aggregate with a nominal
maximum size of 19mm but in no case shall the diameter be less than four times the maximum aggregate
size. The maximum coarse aggregate size in these cores is generally less than 20mm so the 84mm core
diameter used meets this aggregate size requirement. For one set of cores, W2 (i, ii & iii), the maximum
coarse aggregate size is about 25mm so does not strictly meet this core diameter requirement.
4. Results The concrete core results are presented in Table 1.
The core failure mechanisms were all acceptable.
Table 2: Concrete Core Compressive Strength Results
PAGE 3 OF 7 www.opus.co.nz
Core Identifier Compressive Strength
(MPa)
Comments
C1 (i) 8.0 Weak porous concrete lacking in aggregate
C1 (ii) 15.5
C2 (i) 20.0
C2 (iii) 24.5
S1 (i) 40.0
S1 (ii) 37.0
S2 (i) 18.5
S2 (ii) 20.0 Nominally 16mm diameter round bar across core diameter. No
apparent impact on strength result.
S2 (iii) 24.5
S3 (i) 22.0
S3 (ii) 21.5
W1 (i) 7.0
W1 (ii) 8.5
W1 (iii) 8.5
W2 (i) 37.5
W2 (ii) 34.0
W2 (iii) 34.0 Nominally 10mm diameter round bar across core diameter. No
apparent impact on strength result.
W3 (i) 6.0
W3 (ii) 7.0
W3 (iii) 9.0
Prepared by:
Sheldon Bruce
Manager Asset Performance
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Basis of Seismic Assessment C.1 Seismic Loading
The seismic design actions have been determined in accordance with NZS1170.5:2004 with the following
assumptions:
� Importance Level 3 structure (buildings that as a whole may contain people in crowds) and a Design Life
of 50 years.
� Site Location – Rotorua
� Subsoil class category D for the main structure and Subsoil class C for parts loading (due to conflicting
results from previous geotechnical reporting of the site subsoil class we have adopted the more onerous
soil class).
Only the Ultimate Limit State (ULS) loading are considered in the seismic assessment, which is concerned
with life safety of the occupants and collapse prevention.
C.2 Dead and Live Loads
The following basis has been used in establishing the seismic mass for the structure:
� Reinforced concrete for floor slabs, columns, beams and walls is normal weight with a density including
reinforcing of 2400 kg/m3, and in instances where the walls are pumice concrete a density including
reinforcing of 1800kg/m3.
� Structural steel is a normal weight steel with a density of 7600 kg/m3.
C.3 Assessment Assumptions
The key assumptions made during our assessment were as follows:
Item Assumption Comments
Steel grades fy= 228 MPa
fy= 255 MPa
fy=275 MPa
fy=300 MPa
fy=500 MPa
All reinforcing bar, used in the original 1930’s construction of SHMPAC.
All reinforcing bar, used in the 1950’s alteration works.
All reinforcing bar, used in the 1970’s alteration works.
Bar grade called up on the relevant drawings in the 1990’s alteration works.
Bar grade called up on the relevant drawings in the 1990’s alteration works.
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Item Assumption Comments
Concrete strength
(Note: Concrete core strength tests were undertaken as part of the intrusive investigations. This assessment incorporates these results where applicable).
f’c=7MPa
f’c=20MPa
f’c=25MPa
f’c=35MPa
Pumice concrete used in the original 1930’s construction of SHMPAC.
Reinforced concrete used in the original 1930’s construction of SHMPAC.
Reinforced concrete used in the 1950’s alterations.
Reinforced concrete used in the 1970’s and 1990’s alterations.
Element Capacity Assessments Using probable material strengths and a hand analysis
This was carried out following the recommendations of the Engineering Assessment Guidelines.
Structural Analysis 3D Elastic Model in ETABS
2D Models in Space Gass of lateral resisting systems
ETABS models used to analyse force distribution between the various structures.
Period and demand of the building under seismic loading explored
Diaphragms Timber sarking roof diaphragms
Reinforced concrete floor diaphragms
Loads distributed based on tributary width.
Accidental Eccentricity Included in the assessment of the global system. Not considered important in the assessment of the areas with the flexible roof diaphragm.
Modelling Centreline beam and column modelling used
No rigid offsets used. This is conservative for drift.
The achievable seismic rating of the various structural elements has been estimated using the approach
described in the Engineering Assessment Guidelines.
C.4 Seismic Mass
The seismic mass has been computed adopting the NZS1170.5:2004 loading combination W = G + ΨE Qu =
G + 0.3Qu, for floor loading and G, with Ψ=0 for roofs not used for floor activities. No area reduction factor
was used to calculate the ultimate live load Qu, as a conservative assumption.
The seismic mass was determined for each of the areas and distributed equally to nodes in the computer
model
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C.5 Seismic Coefficient
For the analysis of load distribution using ETABS, a building period of 0.4 seconds was assumed in each
direction. For particular elements that were considered using 2D space gass models with flexible diaphragms
the period was determined using the simplified Rayleigh method. In most instances the period of these
individual frames was approximately 1 second.
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Appendix D
Building Inspection Photographs
Photo 1: Main foyer looking east towards the mezzanine and western end of the Auditorium
Photo 2: Main Foyer roof space looking south along the truss that spans between the north andsouth wings on grids 14 and 15. The truss chord members are indicated on the left of the truss spanimage.
Photo 3: Concert Hall end wall (grid 18) looking west. This end wall has previously beenstrengthened with 200mm shotcrete.
Photo 4: Timber sarking roof diaphragm at the eastern end of the Concert Hall. There isapproximately a 10mm20mm gap between the diaphragm and wall. No dependable connection tothe end wall was discovered.
Photo 5: Supper Room looking east into the Kitchen. The wall in the foreground is an unreinforcedpumice concrete block wall.
Photo 6: Supper Room roof space looking west at the timber roof beam and connection into theAuditorium column.
Photo 7: Timber sarking roof diaphragm running north/south in the north wing
Photo 8: Function Room looking south towards the North Wing. The wall/frame in the foregroundis the northern elevation of the North Wing.
Photo 9: Looking east in the Kitchen between grids B and C at the eastern end of the north wing.
Photo 10: Main Auditorium Looking west.
Photo 12: Auditorium roof trusses on the northern side of the Auditorium.
Photo 11: Heavy cables in the Auditorium roof space, at the eastern end.
Photo 13: Main Auditorium roof space looking south along a cut made in the timber sarking roofdiaphragm. Cut out dimensions are: 400mm wide x 8000mm long.
Photo 14: South western side (grid H and grid 4) of the Fly Tower, looking west.
Photo 15: Dressing Room/ Back of House column on the eastern elevation of the Fly Tower (Gridline 2). Deformed bars as shown in the drawings.
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Appendix E
Structural Drawings
Provided separately due to the
large number of drawings